Method and apparatus to operate a high-voltage DC transmission system (HVDC) with automatic control of the converters

ABSTRACT

In a first station operating as the rectifier, a fault indication quantity can replace the measured value of the HVDC voltage which regulates a control voltage. In normal operation in a second station of an HVDC transmission system operating as an inverter, a fault indication quantity is calculated from a control angle and the inductive D.C. voltage drop is calculated from the D.C. current and the A.C. voltage. In the second station operating as the inverter, the overlap angle can be precalculated from a fault indication quantity so that by automatic control of the control angle a preset extinction angle can be assured. Thereby stable, quickly controllable operation without any remote control signals is assured and rapid resumption of operation following a malfunction facilitated.

CROSS-REFERENCES TO RELATED APPLICATIONS

This application is related to the following co-pending applications:

"Method and Apparatus for High-Voltage D.C. Transmission With a Bypass Circuit for Malfunctions" by H. Neupauer, G. Wild and W. Kaufhold, U.S. Patent Office Ser. No. 706,755.

"Method and Apparatus for Resumption of Normal Operation of a High-Voltage D.C. Transmission Line" by Helmut Neupauer, U.S. Patent Office Ser. No. 706,754.

BACKGROUND

This invention relates to the field of High Voltage Direct Current transmission line apparatus connecting two alternating current systems and more specifically to a method and apparatus to control or regulate the system-synchronous converters of a HVDC system.

In such a HVDC system the converter of one station, A, impresses the HVDC transmission current while the converter of the other station, B, determines the HVDC transmission voltage. The operation of the current impressing station, as will be explained in greater detail below, is a function of the HVDC voltage produced by the other station used as a fault indication quantity, whereas the operation of the voltage-determining converter must take into account the impressed current in determining its commutation times.

Each converter thus requires information regarding the operating status of the corresponding other converter. For long distance transmission in addition this mutual interlinkage of the converters is further characterized by having a lag time, namely the travel time of the HVDC, so that stable operation is hard to attain, particularly if the mutual information transmittal is handled by remote control lines having additional transmittal and processing times.

The purpose of this invention is to provide the information required in the simplest possible fashion to assure stable operation and to process the information in the converter stations.

SUMMARY OF THE INVENTION

Briefly stated, in accordance with one aspect of the invention, the foregoing object is achieved by providing a method and apparatus based on the overall structure of the HVDC transmission system taking into account the co-called inductive voltage drop of the converter operating as an inverter. This method and apparatus provides, in the case a short coupling HVDC transmission line system, an automatic control apparatus which permits operation without measuring of the HVDC voltage. This same method and apparatus provides, in the case of a remote HVDC transmission line system, operation without remote control lines and permits stable operation, despite the HVDC lag times, such that the system requires only a short control time periods, thereby permitting a highly dynamic operating procedure and also rapid run-up of the power transmission following a malfunction.

BRIEF DESCRIPTION OF THE DRAWINGS

While the specification concludes with claims particularly pointing out and distinctly claiming the subject matter which is regarded as the invention, it is believed that the invention will be better understood from the following description of the preferred embodiment taken in conjunction with the accompanying drawings:

FIG. 1 shows the design of a HVDC transmission line system.

FIG. 2 shows the relationship between firing angle α, extinction angle γ, the inductive d.c. voltage drop, the d.c. voltage and the a.c. voltage when using a converter synchronous with the system.

FIG. 3 is the schematic design of a HVDC transmission line short coupling with automatic control of the control angle for normal functioning operation.

FIG. 4 shows the configuration of the HVDC transmission system in accordance with FIG. 3.

FIG. 5 shows a modified design of a HVDC transmission system with automatic control.

FIG. 6 shows another schematic design of a station, B, with automatic control.

FIG. 7 is a design modified from FIG. 3.

FIGS. 8 and 9: are modified designs of a station, B, in contrast to FIG. 6.

FIG. 10 shows another schematic design of a station, A, with automatic control.

FIG. 11 is a design of a monitoring device for either a station, A, or a station, B

FIG. 12 or 28: are signal patterns and design of a type of limit value warning device for the monitoring unit in accordance with FIG. 11.

FIG. 13 shows the use of a network model in a station with a HVDC remote transmission line.

FIG. 14 shows the design of the network model of FIG. 13.

FIG. 15 shows the detailed design of a station using a station, B, as an example.

FIG. 16 are signal patterns for operation of a station, B, in accordance with FIG. 1 when resuming the system-synchronous operation after a shutdown of the HVDC transmission line.

FIG. 17 shows the circuitry of a clamping circuit for the arrangement as shown in FIG. 1.

FIGS. 18 and 19 show the patterns of currents and voltages as well as current transit times for the converter thyristors when operating according to FIG. 16.

FIG. 20 shows signal patterns for operating a station, B, in accordance with FIG. 1 in case of a temporary malfunction, i.e., transition from normal operation and into normal operation.

FIG. 21 shows the circuitry of a selector switch in the design according to FIG. 15.

FIG. 22 shows the pattern of a returning a.c. voltage following a system malfunction and the system-synchronous firing pulses of the station as shown in FIG. 15.

FIG. 23 shows the patterns of control angles, voltages and currents in a preferred example.

FIGS. 24 and 25. show the patterns of voltages, currents and signals when operating a HVDC transmission line with a de-energized length during a malfunction of a station, B, or station, A.

FIGS. 26 and 27 show the same patterns in the event of emergency bypass operation during a malfunction of a station, A, or a station, B.

DETAILED DESCRIPTION

FIG. 1 shows an a.c. system, NA, connected to a HVDC transmission line via a station, A, and an a.c. system, NB, connected to the HVDC transmission line via a station, B. Both stations contain a converter. If using this arrangement d.c. current is to be transmitted from the first station, A, to the second station, B, then the current flowing through the HVDC transmission line will be preset by having the first converter located in the station, A, operating as a rectifier in order to draw from the first system, NA a current at voltage U_(A). The output d.c. current i_(dA) of the converter of the station, A, is then impressed into the HVDC transmission line. The second converter located in the station, B, operates in this mode as the inverter in order to supply the input d.c. current i_(dB) received via its d.c. connections into the second system, NB, with the inverter control angle used for the current feed controlling the input d.c. voltage U_(dB) of the station, B, and thus the voltage level of the HVDC transmission line.

Generally, efforts are made to operate the converter with low levels of harmonics, for which reason the converters are designed as 12- and more-pulse converters containing numerous d.c. current side series-connected component converters, for example, connected to the HVDC transmission line using converter reactance coils LA or LB and/or filter circuits (CFA, LFA and CFB, LFB, respectively) and connected to the respective a.c. voltage system, NA or NB, using converter transformers with differing circuits characterized by their transformation ratio u where typically u=1. Particularly for short couplings serving to link two closely adjoining systems and often containing only a high-voltage smoothing reactor, the use of the filter elements LFA, CFA and LFB, CFB respectively can often be omitted. The current appearing following the filtering elements is called the HVDC transmission line current and is designated with i_(dLA). The corresponding HVDC transmission line voltage is designated U_(dLA), while the quantities before the filter elements are designated by i_(dA) and U_(dA).

The actual values required for control purposes are generally obtained as close as possible to the HVDC transmission line connection point of the respective station, i.e., possibly behind the filter units; in other cases, e.g. to monitor the HVDC transmission line under operating conditions, it is irrelevant where the (not depicted) measurement units required to obtain the actual values are installed. The component current converters 1A', 1A" are series-connected on the d.c. current side to connect poles 2,3 of the HVDC transmission line and each contains one output phase R, S, T of the thyristor groups corresponding to their transformers designated by "+" or "-", if respectively their anodes or cathodes are connected to the transformer. Thus, for example, thyristor group R⁺¹ is located in the direction of current flow between the transformer and pole 2. A drive unit supplies the component current converter 1A' with the firing command sequence S'α which consists of the individual firing commands R^(+') α . . . T^(-') α and is either disabled by a clamping circuit shown by switch symbol BS' or amplified to form a firing pulse sequence Z'α as individual impulses R^(+') . . . I^(-') connected to the thyristors designated with the same symbols.

The drive unit ST'_(A) contains a reference voltage system U'_(Asyn) from a reference voltage generator RG'_(A) connected to the a.c. voltage input of the component current converter, which forms the firing commands S'α by comparing U'_(Asyn) with a control quantity, e.g., a control voltage U_(STA) or a control angle α_(A). System-synchronous operation is achieved when control angle equal α_(A).

The control quantity, for example, control angle α_(A), is supplied by a control device 4A and according to the state-of-the-art is generally shared by all component frequency converters of the station. The component current converter 1A" with thyristor groups R⁺ " . . . T⁻ " and its control devices RGA", STA", BS", is designed in the same way as the component current converter 1A'; similar quantities are designated accordingly. As in most cases it is obvious to those skilled in the art how to control the existing component frequency converters by using the control quantity of the station, A the overall current converter is often designated as 1A in the following description and the differentiation of the quantities assigned to the respective component current converters suppressed.

The station, B, is designed analogously as far as possible; the component frequency converters 1B' and 1B", for example, are often treated as one single converter 1B. As many structural components and design features are identical for both stations, the differentiation using the letters A and B is omitted in these cases.

In the converter 1A operating as a rectifier, the control angle is preset near the wide-open setting (α_(A) ≐0) and initially controls the output d.c. voltage U_(dA). The output current i_(dA) is then determined by the voltage drop U_(dLA) -U_(dA) at the filter choke coil LA according to the following equation:

    i.sub.dA =1/LA∫(U.sub.dA -U.sub.dLA)dt                (1)

Thus, if a control quantity i*_(dA) is fed to the control and regulation unit 4A as a set value for a current control supplying the control angle α_(A), then the collapse of voltage U_(B) or U_(dB) as, for example, brought about by an inverter failure in the station, B, or any other change in the operation of the station, B, after the HVDC transmission line travel time, results in a change in U_(dLA) resulting in a current change and excitation of the current controller.

For current control of the station, A, thus U_(dLA) or with the lag time determined by the HVDC transmission line travel time U_(dB) operates as the fault indicating quantity.

The situation is similar if the active power to be transmitted is used as the control quantity of the station, A. In this case an active power controller supplies, for example, the set value i*_(dA) in accordance with the active power nominal value P*_(A) coodinated with the energy balance of the system, NA.

Also, the d.c. converter 4B of the station, B, determines by its control angle α_(B) the output d.c. voltage U_(dB). As the d.c. current i_(dB) supplied as active and reactive current into the system, NB, is impressed by the station, A, the control and regulation unit 4B can control the reactive output into the system, NB, in accordance with a reactive power set value Q*_(B) which can be used as the control quantity to stablize the system voltage. Thereby the station, B determines which voltage level will be established in the HVDC transmission line. The current i_(dB) and the current flow in the system, NB, develop freely; it corresponds, except for slight resistance of losses to the conductor, to the impressed current i_(dA) defined prior to the line travel time.

As particularly for a high active current component of the transmission a control angle normally near the inverter wide-open control setting (α_(B) near 180 degrees) is the goal, the time lapse during commutation from the firing of the succeeding thyristor (firing angle α_(B)) until complete deactivation of the preceding thyristor (i.e., up to the extinction angle, γ_(B)) is relatively long and increases as the current i_(dB) rises. During the commutation time the voltage U_(dB) collapses by a so-called inductive d.c. voltage drop.

The inductive d.c. voltage drop brought about by the d.c. current i_(dB), or the impressed current i_(dA), thus functions as the fault indicating quantity for converter d.c. converter 4B.

This is particularly important since the extinction angle must not exceed a maximum value, inverter step limit, which depends upon the release time of the converter thyristors so that no inverter failure with short-circuiting of voltage U_(dB) arises. An increase of the impressed current i_(dA) produces, after the HVDC transmission line travel time, an increase of the commutation time in the station, B and an increase of the inductive d.c. voltage drop which has to be dealt with by an advance of the firing time point of station, B, i.e., reduction of α_(B), if the maximum extinction angle or a preset extinction angle γ* used as the control variable of the station, B, is to be adhered to.

Due to these mutual control fault indicating quantities the controls of the converters coupled to each other using the HVDC transmission line have to be coordinated in their operation. Generally, information regarding the operating status of one converter, e.g., a marginal current signal or a malfunction signal derived from the respective control quantity, is transmitted to the other station using remote control lines. Due to the travel time of the HVDC transmission line as well as the processing time for this information transmission, stable operation of the HVDC transmission line can only be attained if the controllers of both stations are set relatively slowly, e.g., on/off control times of 200 ms for example.

The HVDC transmission line can thus stabilize the relevant a.c. voltage systems given rapid malfunctions to a limited extent only. Moreover, rapid startup of the HVDC transmission line, in particular given a transitory malfunction in a station and thus a temporary failure of the HVDC transmission line for example, is not possible. Thus, for example, provision of an adequate safety margin from the inverter step limit is intended primarily to avoid an inverter failure at the expense of a reduction in the active power transmission.

The operating procedure described below reduces these problems. It permits, given adequate protection against inverter failure, highly dynamic control and rapid startup after malfunctions.

Thus, initially the formation and transmission of the information specified is simplified and by suitable measures, namely automatic control of the control angle of one station using the fault indicating quantity or else a model value to be considered, the starting control times are substantially shortened. In the case of a HVDC transmission line short coupling in which, due to the close proximity of both stations, the information regarding the operating status of the other station is available without extended transmission times; a d.c. voltage detector for the HVDC transmission line voltage is no longer required.

In a HVDC line long-distance transmission the information required in one station regarding the other station is practically formed by the operating quantities only, particularly actual and set values, of the one station. Thereby remote control lines are omitted and the information is available at the earliest possible point in time, namely as soon as the status change of the other station is noticed in the former station. The automatic control apparatus thereby initiates very rapid closed loop control circuits, with startup times of less than 50 ms, e.g. 20 ms, becoming feasible.

If the operating uncertainty, due to the model fault indicator quantity used, occassionally leads to inverter failure or to another converter malfunction, the economic consequences of such a malfunction can be held to a minimum since the automatic control utilized permits a rapid restart of the HVDC transmission line following a malfunction. Thus the operating procedure can be coordinated primarily for optimum utilization of the HVDC transmission line. In particular, the HVDC transmission line can also be designed to stabilize dynamic processes, e.g., balancing processes in the systems, primarily in order to stabilize the system voltage. Particular design features further permit this utilization of the HVDC transmission line even when due to a malfunction of a rectifier or inverter the active current transmission is interrupted.

The Inductive D.C. Voltage Drop As the Fault Indication Quantity

The method in accordance with this invention is based upon an investigation of the effect that d.c. quantities of a converter have on its operation.

FIG. 2 depicts in broken line the voltage patterns of the individual phases of an a.c. system, i.e., system voltage U≈. Assuming that the current in the converter is commuted immediately and completely when the thryistor is fired, the voltage u_(di)α (t) dependent upon the firing angle α arises at the d.c. connections which is designated as the instantaneous value of the ideal unsmoothed no-load direct voltage.

The ideal-type assumption that the current is immediately commuted, so that the commutation time span is zero, is present only under no-load conditions in which the d.c. current itself becomes zero. Given wide-open control setting, the average value of the ideal no-load direct voltage under these ideal conditions is the voltage U_(di) which is proportional to the momentary system voltage amplitude U≈ or the effective system voltage in accordance with a definable ratio which is a pure numerical value for the respective converter type:

    U.sub.di =const·U≈                        (2)

i.e.,

    U.sub.diA =const·U.sub.A, U.sub.diB =-const·U.sub.B

The change in the value for the station, B, takes into account the reversed current orientation of the thyristors of converter 1B in contrast to the numerical orientation of voltage U_(dB). U_(di) responds to the voltage vs time waveform of the rectified system voltage.

The respective ideal unsmoothed no-load direct voltage u_(di)α (t) and u_(di)α (t) correlate to the two firing angles α and δ. Their integrated voltage vs time waveforms shown crosshatched are given as smoothed ideal no-load direct voltages by:

    U.sub.diα =U.sub.di cos α, U.sub.diα =U.sub.di cos δ

Turning now to actual conditions, it is assumed that the converter with firing angle α is fired and that the current i_(d) actually flowing via the thyristors in the d.c. voltage supply requires a certain commutation time, e.g., corresponding to an overlapping angle u during which both thyristors are current-conducting, in order to pass out of the previously fired thyristor. The end of the commutation time is specified by the angle δ, i.e., the extinction angle γ=180°-δ so that the following applies:

    180°-γ=α+u                              (4)

whereby the positioning of the extinction angle γ, i.e., the value of the overlapping angle u, depends upon the magnitude of the commutating current i_(d). The unsmoothed d.c. voltage u_(d)α (t) actually arising at firing angle α is also depicted in FIG. 2. It is practically the average value 1/2. (u_(di)α (t)+u_(di)α (t)) which the voltage-commutation vs. time slot depicted crosshatched on the right divides in half. Thus, for the actual average value U_(d)α of the d.c. voltage

    U.sub.dα =1/2(U.sub.diα +U.sub.diα)=U.sub.diα -1/2(U.sub.diα -U.sub.diδ)                    (5)

i.e., the actual d.c. voltage deviates from the ideal no-load direct voltage U_(di)α =U_(di) cos α corresponding to the firing angle α by a voltage differential. This so-called inductive d.c. voltage drop is proportional to the actual d.c. current i_(d) via a converter-specific parameter dx:

    1/2(U.sub.diα -U.sub.diδ)=dx·i.sub.d =1/2U.sub.di (cos α+cos γ)                                      (6)

so that the following relationships prevail: U_(d)α =const·U≈cos α-dx·i_(d), i.e., given suitable standardized measurement values U_(A) and U_(B) for the a.c. voltage amplitudes in both stations, the following equations apply for the HVDC transmission voltages U_(dA) and U_(dB) :

    U.sub.dA =U.sub.A ·cos α.sub.A -d.sub.XA ·i.sub.dA

    U.sub.dB =-U.sub.B ·cos α.sub.B -d.sub.XB ·i.sub.dB

It should be noted that d_(XB) is a negative quantity due to the defined polarity of i_(dB) and U_(dB).

As due to the existing inductances the d.c. current practically does not change during a commutation, equations 4 and 6 permit a precalculation for each firing time point based on the firing angle and the measurement values for the a.c. voltage and the d.c. current with regard to the values that the overlap angle, the extinction angle and the d.c. voltage will assume during firing.

Normal Operation with Automatic Control

The first application of these relationships is depicted in FIG. 3 for a short-coupling arrangement, i.e., the HVDC transmission line consists in this case only of one inductance L=LA+LB, arranged without filtering circuits between the two converters 1 and 2. FIG. 4 depicts the structure of this arrangement, whereby inductance L of the HVDC transmission line analogously to equation 1 is depicted by an integrator having integration constant L and with the input value U_(dA) -U_(dB) and the output value i_(d) ≐i_(dA) ≐i_(dB).

The action of converter 1A of drive unit STA and of the reference voltage generator RGA depicted as the current-impressing assembly SRA is determined by the fact that the set firing angle α_(A) given with incomplete synchronization of the reference voltage generator to the actual phase of the a.c. voltage of NA determines the voltage U_(di)αA /U_(A) =cos (α_(A) +δα_(A)) except for an angle error δα_(A) (cos generator 410 in FIG. 4). By renormalizing (multiplier 411) and taking into account the inductive voltage drop d_(XA) ·i_(d) of this converter (proportional element 413, subtraction element 412), one eventually obtains U_(dA) =U_(di)α -i_(d) d_(XA).

The lag time of the current impressing is symbolized by lag time circuit 414, while a dynamic circuit 415 shows the smoothing of the control angle in the drive unit or in a generally advantageous integral drive unit smoothing mechanism.

This demonstrates that the inductive voltage drop of converter 1A can be compensated in accordance with the principle of automatic control by the addition of a corresponding model control voltage d_(XA) ·i_(d) to the control quantity for U_(A) (in this case the signal U_(A) ' cos α_(A) * supplied by a current regulator 41A). In many cases, e.g., if a U_(A) normalized arcos-function network 40a is connected following the controller 41A to linearize the control characteristic function, the normalization of the automatic control voltage, model fault indication quantity, corresponding to the normalization of the control quantity is not even necessary so that computing circuit 43A only requires a proportional circuit 431' in order to form the model fault indicator quantity i_(dA) x·d_(XA) from the available current-measurement value i_(dA) (in this case i_(dA) ≐i_(d) ≐i_(dB), i.e., a quantity available at the location of the station, A).

If one connects in addition or as an alternative to the automatic control device (additional element 42A) the voltage U_(dB), then also the effect from the converter 1B on the current control will be compensated. The station, A, thus compensates, practically without any delay, jumps in the fault indication quantity, coming from The station, B, and the controller can be more rapidly adjusted since thereby the delaying effect of the HVDC transmission inductivity is obviated. Correspondingly, the controller can be optimized strictly in terms of the time behavior of the current impression (actual value and set value generation as well as smoothing and delay of the converter) without considering the time constants to be allocated to the transmission conductor and the operation of the station, B.

The HVDC current transducer basically required for this operation can, however, be omitted in accordance with the invention if the actual value U_(dB) for the automatic control is replaced by a model fault indication quantity U_(dB) computed by a computing circuit 44 from the measured value i_(d), i.e., the HVDC transmission current or the input d.c. current of the converter 1B in accordance with equation (7):

    U.sub.dB =-U.sub.B ·cos α.sub.B -d.sub.XB ·i.sub.dB

from the actual value i_(dB), the system voltage U_(B), and the firing angle, control angle α_(B). In accordance with the circuitry symbols (FIG. 3) a proportional link 442 and multiplier 441 and a summation point 443, for example, serve that purpose.

In this context, however, the time behavior of both converters with their drive units and the HVDC transmission line itself must be taken into account. This is handled by a dynamic element 440 which is preferrably designed as several smoothing links connected in series and therefore permits, in particular, adequate consideration to be given to the resulting lag times.

In summary, the converter 1A is operated with a control angle α_(A) forming part of a control voltage U_(STA) =U_(A) ·cos α_(A) *+U_(dAv), automatic control voltage U_(dA) can take into account the inductive d.c. voltage drop ΔX_(Av) =i_(dA) ·d_(XA), but particularly contains the following fault indication voltage U_(dLA) (for short-circuit coupling: U_(dB) or else U_(dB)) as shown in equation (1).

In the station, B, one must also take into account that the inductive d.c. voltage drop also functions as a fault indication quantity on the voltage U_(d)α determined by the control angle α_(B), in addition to the fault indication voltage caused by a synchronization error δα_(B). This fault indication variable has to be eliminated by the control quantity controller.

The station, B, shown in FIG. 4 contains the same structural components for block SRB with a drive unit smoothing component 415B (if necessary designed as an integral smoothing circuit) and a automatic control device comprising a summing point 42B and, depending upon the nature of the Δ_(XB) signal and the Δ_(XBV) automatic control signal, a linearizing circuit 40B.

As FIG. 8 shows, initially a signal which determines a set value of the HVDC transmission voltage U_(dB) *=-U_(B) ·cos α_(B) * using a preset angle α_(B) *, can be taken from a control device which computes this voltage set value from a control quantity or other operating values of the station, B, (controlled operation). In particular, however, α_(B) * (or cos α_(B) * if a linearizing circuit 40B is also connected) can be obtained as the output signal of a control quantity controller.

The corresponding model fault indication quantity is then connected to the automatic control device (summing point 59, FIG. 8) as an inductive d.c. voltage drop d_(XB) ·i_(dB) (or as the corrsponding automatic control angle) and onto this preset angle in such a way that the control angle α_(B) is determined by α_(B) =α_(B) *+α_(Bv), with cos α_(B) =U*_(dB) +d_(XB) ·i_(dB) /(-U_(B)). In the circuit component SRB, the control command for the inverter thyristors is generated by a reference angle Φ(t) of the reference voltage generated by the reference voltage generator RG_(B) which is defined by the condition

    (U*.sub.dB +d.sub.XB ·i.sub.dB)/(-U.sub.B)=cos (α*.sub.B +α.sub.Bv)=cos Φ(t)

or

    α*.sub.B +α.sub.Bv -Φ(t)=0

Thereby a jump in the fault indication quantity can be largely and virtually immediately compensated even if the control quantity controller 41A generating the fault quantity is adjusted very rapidly, e.g. time constant less than 50 ms, particularly approximately 10 ms or less. Here as well the controller can be optimized strictly in terms of the time response of its own station without taking into account the time constants to be attributed to the HVDC transmission line and the other station.

Although this does permit stable stationary operation with rapid control functions, it does not assure the maintenance of a corresponding minimal extinction angle or safety angle corresponding to the inverter step limit.

However, to avoid inverter failure, the commutation always has to be completed at a certain, i.e., minimum extinction angle γ*. Therefore the thyristors must always be fired at a phase position Φ(t) of the inverter defined by:

    Φ(t)=180°-γ*-u

In the ideal instance in which the thyristor firing takes place without switching delay and with ideal synchronization at the phase position Φ(t)=α_(B), with the voltage drop being exactly obtained by the model value d_(XB) ·i_(dB) /(U_(B)), the control angle α_(B) then must be limited to (α_(B))_(max) =180°γ*-u=arcos (-cos γ*-2d_(XB) ·i_(dB) /(U_(B)).

In operating conditions in which said firing angle limitation prevails, the firing condition Φ(t)=180°-γ*-u, 180°-γ*-u-Φ(t)=arcos (-cos γ*-2d_(XB) i_(dB) /U_(B))-Φ(t)=0

or

    -cos γ*-(2d.sub.XB ·i.sub.dB)/(U.sub.B)-cos Φ(t)=0

accordingly applies in the drive unit with γ* or else cos γ* being a value for the extinction angle which is preset. This presetting of the maximum control angle α_(Bmax) can be handled by a limiting device 58 (FIG. 8) at the input channel for the control angle α_(B) of the drive unit, with α_(B) being preset by a control function and, as was just explained, capable of being set by automatic control. The limitation thereby also functions as an automatic control with an automatic control angle α_(Bv) =(α_(A))_(max) computed from γ*.

If equation 7 applies strictly and a set angle γ* is calculated and limited to γ_(min) from the voltage set value U*_(dB) by U_(B) cos γ*=-U*_(dB) +d_(XB) ·i_(dB), then the angle γ* formed in computing stage 43B' (FIG. 8) equals α_(Bv) =arcos (-cos γ*-2d_(XB) ·i_(dB) /U_(B)) or, if no linearization is performed, the corresponding voltage U_(dBv) =-U_(B) ·cos γ*-2d_(XB) ·i_(dB) provides a limit value for the angle α*_(B) or a correponding control voltage which can be preset in any desired fashion e.g., by a reactive current controller or another control quantity controller.

Said control quantity controller can then simply cause the control angle α_(B) and thus the voltage U_(dB) in contrast to the automatic control angle α_(Bv) to be retracted while with given U_(B) and i_(dB) the values U*_(dB) and γ_(min) will not be exceeded. If the angle γ* can be calculated from the control quantity set value as takes place in computing element 47 of FIG. 6 or 7, then the angle α_(Bv) =180°-γ*-u can be directly connected to the drive unit in a controlled arrangement without any further adjustment.

In the drive unit the following always applies:

    α.sub.Bmax =180°-γ*-u

wherein u is the computed overlap angle from γ* and the inductive d.c. voltage drop (model fault indication quantity).

The model value 2d_(XB) ·i_(d) /(U_(B)) can thereby be determined from momentary values for i_(d) and U_(B) for each phase position of the system. This means that for each momentary phase position of the system the respective inductive voltage drop and thus the overlap angle will be precalculated. By monitoring the specified firing conditions, therefore, a thyristor firing will be initiated if in accordance with the precalculated overlap angle the still remaining time period until the set time point of a thyristor extinction (predetermined by γ*) suffices to complete the commutation.

In actual converter operation a control angle controlling signal α_(Bv) calculated from a set extinction angle γ* in accordance with 180°-γ*=α_(Bv) +u causes at the reference angle Φ(t) a thyristor firing which, however, takes place at the actual phase position Φ_(o) (t)=Φ(t)+δΦ.sub.α of the a.c. voltage system and, due to a possible imprecision δu of the computed overlap angle leads to the actual value 180°-γ=Φ(t)+δΦ.sub.α +u+δu. Thus, there is a set/actual value differential Δγ=α_(Bv) -Φ(t)-δu-δΦ.sub.α.

For that reason the differential Δγ is preferrably eliminated using an extinction angle controller 41B shown in FIG. 8, to whose output signal ΔX_(B) the precalculated automatic control angle αBv is added so that for the drive unit we have the following condition:

    ΔX.sub.B +α.sub.Bv =Φ(t) with α.sub.Bv =arcos (-cos γ*-2d.sub.XB ·i.sub.dB /(U.sub.B)

A controller can, however, be used for another control quantity whereby the set extinction angle γ* to calculate α_(Bv) will be determined from the control quantity set value (compare item 47 in FIG. 5 or 6) and the control output signal ΔX_(B) will correct the extinction angle to maintain the control quantity set value.

Here as well, the overlapping angle or the inductive d.c. voltage drop belonging to γ* will be precalculated from momentary values for i_(dB) and U_(B) at each phase position Φ(t).

Thereby one attains a controlled presetting of the extinction angle which is used in FIG. 8 to limit the either controlled or regulated preset angle α*_(B). In the preferred design example of FIGS. 3 and 4 the controlled preset automatic control angle α_(Bv) is connected directly to the control quantity controller 41B output as the model fault indication quantity ΔX_(Bv) whose output quantity ΔX_(B) serves to control the control quantity preset extinction angle in terms of cos γ*-cos γ=0. The automatic control device 42B, 40B is thus in this case connected to the automatic control voltage ΔX_(Bv) =-cos γ*-2·i_(dB) ·d_(XB) /U_(B) to generate α_(B) =180°-γ*-u+ΔX_(B). This automatic control voltage serves thus to take into account the inductive d.c. voltage drop and is computed by the 43B computation circuit which can be handled, for example, by the computation components with the computation circuits shown in the circuitry symbols.

Said taking into account of the relationships here indicated can, of course, also be handled in accordance with deduced relationships in modified computation circuits which those skilled in the art can develop as required.

Thus, in the case of a short-circuit coupling one develops an arrangement coordinated for rapid elimination of operating status changes of both converters which requires only simple mechanisms; particularly the high-voltage component only requires a current transducer as a detecting unit.

In FIG. 5 these relationships are applied to the system in which the converters are connected via converter reactance coils LA and LB and filter circuits LFA, CFA as well as LFB, CFB to the HVDC transmission line (short-circuit coupling or remote transmission line).

This arrangement dispenses with any compensation of the slight control angle shift brought about by the inductive d.c. voltage drop of the converter 1A. Furthermore, to take into account the fault proceeding from the station, B, the HVDC transmission input voltage U_(dLA) is used in place of the model fault indication quantity U_(dB) as the automatic control voltage U_(dAv) in the station, A.

In normal operation the station, A, requires no remote action signals which influence its operation similarly to information transmitted over remote control lines regarding the status of the station, B. Rather, in the station, A, all the required actual or set value quantities required for normal operation are available. The same applies to the station, B. The automatic control of both stations thereby takes into account the mutual coupling of both stations in such a manner that stable operation with short control cycles is attained.

In the design according to FIG. 5, the linearizing circuit 40B is integrated into the computing circuit 43B since an extinction angle controller is used as the control quantity controller 41B, whose output signal ΔX_(B) already defines an angle. The cos γ* required in the computing circuit 43B is then formed using a function generator 40B'.

The design also foresees that given sudden irregular changes in the respective control quantities in both stations, the respective change rate of the control quantity set values can be limited by run-up function generator 45A or 45B. The other components already familiar from earlier figures are identified with the old reference symbols.

In the station, B, optionally either the extinction angle γ, the reactive power Q, or another suitable control quantity can be used to maintain constant voltage, to dampen balancing processes or for other dynamic controls. This is indicated by the selector switch 46, whereby the input of the automatic control device 42B can be switched between the extinction angle controller 41B and other control quantity controllers 41B', 41B". For this switchover the design foresees that an auxiliary computing circuit 47 will supply the relevant extinction angle set value γ* or else the cos (γ*) obtainable from the function generator 40B based upon the control quantity set values utilized in the particular case.

The converter parameters d_(XA) or d_(XB), respectively, required to generate the model fault indication quantity which corresponds to the inductive voltage drop of the converter, can be automatically reset in the relevant computing circuits since always during each thyristor extinction the actual inductive voltage drop is determined from the measured firing and extinction angle and compared with the computed value in accordance with the following relationship:

    U.sub.B (cos α.sub.B -cos γ)=2d.sub.XB ·i.sub.dB.

In accordance with this comparison the parameter 2d_(XB) can then be adjusted as indicated by the parameter feedback device 48 in FIG. 6.

In addition, FIG. 6 symbolically shows that the drive unit STB generates the control signals S.sub.α by monitoring the above-specified firing condition.

The precalculation of the overlap angle which at the momentary phase position Φ(t) of the system always belongs to the set extinction angle γ* as well as the momentary values of i_(dB) and U_(B) can, for example, proceed within a millisecond-frequency in a microcomputer 43B as shown the case of a short coupling (inductivity L) in FIG. 7. Here as well, use is made of the model fault indication quantity U_(dB) as the automatic control voltage U_(dAv) of the station, A, whereby the computing circuit 44 can be further substantially simplified if one starts not from the control angle α_(B) itself, but from the preset extinction angle γ* or related quantities generated in the microcomputer itself. In particular, for example, in place of U_(dB), the quantity U_(B) cos γ*-d_(XB) ·i_(dB) can be connected by a dynamic circuit which imitates the transmission behavior of converters and the HVDC transmission line to the automatic control device 42A. In addition, FIG. 7 shows that preferrably the effective output P of the HVDC transmissions line is used as the control quantity of the station, A. From the control differential p*-p a superimposed active power controller 51 generates the set value i*_(d) of the current regulator 41A. This set value i*_(d) can also preferably be regulated by a fault indication quantity i_(d) at the addition circuit 52 whereby i_(d) =p*/U_(dB) is supplied by the divider 53.

FIG. 8 depicts a design for the station, B, in which the run-up function generator 66B initially supplies a control quantity which (if necessary via a drive unit smoothing circuit 415B) presets the control angle α_(B) of the converter. The quantity α*_(B) can be preset from a non-depicted control quantity controller, e.g., an active power controller or a controller for the HVDC transmission voltage U_(dB) or can be preset in accordance with the already discussed controlled operation by computational means. An automatic control device 59 is shown which compensates the inductive d.c. voltage drop influencing on the set angle α*_(B) which is supplied by a computing unit 43B". The microcomputer 43B" previously shown in FIG. 7 also determines the cosine of an automatic control angle α_(Bv) which takes into account both the voltage difference brought about by the inductive d.c. voltage drop between the ideal no-load direct voltage relative to γ* and the voltage U_(B) as well as the angle shift brought about by the inductive d.c. voltage drop between the angle α_(B) and the ideal firing angle belonging to voltage U_(B).

The linearization circuit 40B' provides a maximum extinction angle α_(max) for a limiting circuit 58 calculated from 180°-(γ*-U+ΔX_(B)), whereby ΔX_(B) is prepared at the output signal of an extinction angle controller 67B.

As long as the limiting circuit 58 is not in operation, the converter is regulated by the preselected value of α*_(B). If, however, the compensated angle α*_(B) attains the preset limit angle α_(max), the extinction angle control intervenes and the converter is operated with the controlled extinction angle. If the extinction angle controller 41B is deactivated, for example, by a short-circuit switch 47B, then only the automatic control angle α_(Bv) determines the limit angle α_(max). By the action of the angle limitation 58, the station, A, is then operated with a regulated extinction angle.

As a rule, the incorporation of the inductive d.c. voltage drop described assures that the inverter step limit is observed as long as i_(dB) and U_(B) do not change all too drastically during a commutation process so that the precomputed transmission angle u coincides adequately with the actual overlap angle. This permits operation with maximum firing angle (maximum active power transmission or minimum reactive power). A greater safety margin to the inverter step limit is thus not required as long as it is assured that even in an extreme case in which sudden changes of i_(dB) or U_(B) can lead to a failure of the inverter, the converter switches over to malfunction operation and after the termination of a malfunction can rapidly resume normal operation.

In the preferred design of the control and regulating device 4B in FIG. 9, a monitoring and programming switch 62B is included which contains a memory circuit 63B (for example, a programmed microprocessor) and a monitoring device 64B which will be described later.

Device 62B activates two selector switches 60B and 61B whose position as shown in FIG. 9 corresponds to normal operation. In this normal operation the automatic control voltage (automatic control angle α_(Bv)) generated by the microcomputer 43B' is connected via switch position P1 to the automatic control device 42B and added to the control quantity ΔX_(B) of firing angle α_(B) which is generated by a control quantity controller, particularly an extinction angle controller 41B. A control device 68B not shown in detail can, be repositioning switch 60B, be connected to the automatic control device so that, for example in emergency operation, the control angle will be generated in accordance with the requirements of the system, NB, (for example, in accordance with a reactive output set value Q*_(B)) required to approximately maintain a constant voltage.

In switch position P2 another model value is supplied to the input of the automatic control device 42B in place of the model value for the model fault indication quantity α_(Bv). Said model value is supplied by a run-up function generator 66B. The end value of this run-up function generator is determined by values preset in terms of the normal power transmission of the HVDC transmission line in trouble-free operation. For example, in accordance with a normal value U*_(B) for the HVDC transmission line voltage computed by a divider 67B as the quotient of the nominal active power P* and the nominal HVDC transmission line current i*_(dB) for normal operation.

Switch position P3 is reserved for a case in which the control angle α_(B) has to be temporarily shifted due to the surging hookup of an additional set value (i.e., to shut down the HVDC transmission line or to pass over into normal operation).

The station, A, is very similar in design with identical components having the same coding numbers along with the letter A as shown in FIG. 10.

Aside from a possibly somewhat different operation of the linearizing circuit 40A, the station, A, is designed so that the selective switch 60A switches the current set value i*_(dA) projected for normal operation for the current regulator 41A to a current set value which is supplied by a superimposed control device 68A in accordance with the requirements of the system, NA, in case of a malfunction. Moreover, in position P1 of selective switch 61A the voltage U_(dLA), i.e., the d.c. voltage obtained when using filtering circuits between the filter circuits and the HVDC transmission line connection of the station, A, is connected to the automatic control device 42A as the model fault indication quantity U_(dAv) in normal operation.

In both stations, moreover, the startup generators 66A, 66B as well as the control variable controllers 41A and 41B can be deactivated by the control and programming circuits. In addition, the design foresees that in the event of a malfunction the devices 62A and 62B transmit relevant malfunction signals to shut down the converter, e.g., by triggering the clamping circuits BS from FIG. 1.

Monitoring Malfunctions

In the normal operation described there are no complications due to delay times and processing times of remote control signals which often necessitate a slow adjustment of the HVDC transmission line operation.

Normal operation of the stations is, however, possibly only if both system, NA, and system, NB and both converters are intact. Should one system or converter fail, the operation has to shift into emergency mode. For that reason both stations require a monitoring device which monitors the correct operation in both stations.

Said monitoring device is depicted in FIG. 11 and will initially be explained in its operation in converter A. Said monitoring and the alternating transition between normal operation and emergency operation given malfunctions should also, as far as possible, be operative without remote control signals. Rather, based upon a further fundamental concept of this invention, the required information regarding interrupted or resumed normal operation in the other station should be recognized from the effects of said operation in the former station. It would therefore be advantageous to generate clearly recognizable signals that the transition in the other station proceed in a certain fashion. While these measures for the transition from and into normal operation will be described later, first the design of the monitoring arrangement based on FIGS. 11 through 14 will be explained.

In these figures the design for the monitoring arrangement of one station only is shown. The other station contains an identical arrangement and the signals F_(de) generated in such an arrangement are, if necessary, to be supplemented by the identifying letter of the station in which they are generated, e.g., F_(deA), F_(dfA) in the station, A.

The advantage of this monitoring device is that it does not require remote control signal lines. The start or the end of a malfunction in the other station is recognized on the d.c. current side input of the first station at the earliest possible moment. If for safety reasons signal lines connect the two stations, then the signals transmitted thereby do not normally directly initiate measures to shut down or start up the first station. Rather, this mode of operation is in the last analysis initiated by the HVDC transmission line currents, e.g., in the station A, by measured values i_(dA) and/or i_(dLA) ; and the HVDC transmission line voltages, e.g., U_(dA) or U_(dLA) ; and the logical combination of the measurement variables, particularly the logical combination of the measured values for amplitude and, if necessary, phase location of the first station's a.c. voltage system.

The monitoring device is moreover also in the position to notify the sound or malfunctioning status of its own station and to store the relevant notification.

The system voltage amplitude U≈ (in case of the station, A, this means voltage U_(A)) is monitored using a limit value warning device 711 to determine whether the preset minimum value required for proper operation has been exceeded; the output signal G₇₁₁ ="1" shows that the a.c. voltage system is intact.

The monitoring signal G₇₁₁ can be used, in particular, to set the output signal Q of a malfunction memory 700 to the Q=1 signal corresponding to proper normal operation. The memory is designed, for example, as a flipflop whose setting input is set by an OR gate 701 using a releasing signal F_(f) which releases normal operation. Said release signal is initially generated when ending the malfunction of its own system by having the resumption of the limit value U_(grenz) impact a time circuit 713 via a delay circuit 712, time constant T_(syn), which thereupon generates a pulse, internal release pulse F_(fe), of a preset length following the preset delay defined by the delay time T_(syn). The delay time T_(syn) takes into account that upon resumption of the first system voltage a certain time is required until its own reference voltage generator can generate the system-synchronous reference voltage required for normal operation of its own converter from the returning system voltage.

If, however, during a system malfunction, the system's own voltage drops below the limit value, then from G₇₁₁ ="0" a pulse F_(de) (internal malfunction warning pulse) is generated using assembly 74 which as its key element contains a further time circuit 741, which passing through an OR gate 702 activates the reset input of the malfunction memory 700 with the corresponding malfunction signal F_(d) =1. The OR gate 701 and 702 can also receive other suitable malfunction or release notifications using further inputs whereby other critical quantities of its own a.c. voltage system, e.g., impermissible changes of frequency or phase, are monitored. The limit value warning device 711 and the other monitoring circuits to detect and monitor its own a.c. voltage can be accommodated thereby particularly in the reference voltage generator utilizing the signals generated therein anyway. For example, the proper operation of its own converter can thereby be monitored or, using a start command, the system can be brought on line from a standstill.

The signal status Q=1 set by the release signal F_(f) indicates not only the undisturbed status of its own station, but also of the entire system. Correspondingly, the signal status Q=1 indicates a malfunction and is set by the malfunction signal or defect signal F_(d).

For that purpose the output of components 71 and 74 which monitor their own station are logically combined with an external release pulse F_(ff) or an external malfunction warning pulse F_(df) using the OR gates 701 and 702 to the release signal, F_(f), or to the malfunction signal, F_(d). These impulses F_(ff) and F_(df) are generated by the component 73 or 72 integral to their own station and notify by monitoring the electrical variables at the d.c. voltage connections of their own station that the other external station has respectively gone into normal operation or a malfunction-reflecting emergency operation. Insofar as its own system is operating properly, the pulses F_(ff) and F_(df) thus initiate the suitable operation of their own station depending on the functioning or malfunctioning status of the other station.

An external malfunction, for example, always exists if in the external station a short circuit of the system or of the converter occurs and therefore the d.c. current passes through this short circuit as fault current. Said fault current is noticable in its own station after a delay reflecting the travel time of the HVDC transmission line in that the d.c. current i_(d) deviates substantially from the current set value defined for normal operation; the deviation i_(d) *-i_(d) exceeds critical values. This also occurs if given long-term malfunctions the line is dead and therefore the current at the d.c. voltage side connections of the station in question no longer reacts to the control.

For that reason, in component 72 detecting the external malfunction the design incorporates a subtraction circuit 721 to generate the difference i*_(d) -i_(d) in its own station as well as a connected rectifier 722. A connected bandpass filter sees to it that short-term power deviations, particularly those arising during the commutation times of its own converter, are suppressed in the same way as constant or relatively long-term deviations. Said long-term deviations arise, for example, when starting up to normal operation before the HVDC transmission line can transmit the complete d.c. current i*_(d) following a malfunction. A suddenly appearing increase or drop of the d.c. current extending for several milliseconds is noticed at the output of filter 723 and registered by a limit value warning device 734. Since said malfunction also arises if the local station itself is malfunctioning, the output signal of the limit value warning device 724 is only released to an AND gate 725 if, for example, using the limit value warning device 711, the normal status of the local station has been reported.

If, on the other hand, the external station has resumed normal operation after eliminating an external malfunction, then this becomes noticable in the station in question after a delay due to the travel time of the HVDC transmission line by means of a sudden change of voltage and/or current at the d.c. current connections. Therefore, for example, the input d.c. voltage U_(d) or U_(dL) (for example U_(d) =U_(dA), U_(dL) =U_(dLA) for the station, A is differentiated using a differentiation circuit 733 in order to generate subsequently an external release pulse in a limit value warning circuit 734 as soon as the voltage change has exceeded a certain limit value. The output signal of this limit value warning circuit 734 can, in turn, be connected to an AND gate 732 if assembly 71 reports a malfunction of its local system.

In this connection it can be advantageous to generate the required external release pulse F_(ff) also by a corresponding monitoring of the current by elements 730, 731, 735.

A limit value warning circuit 734 can be designed in accordance with FIG. 12 to increase the reliability for the detection of resumed operation in the external station. The changes in the electrical quantities (e.g., U_(dB)) brought about by a resumption of normal operation by the external station (in the example of FIG. 12: the station A) at the d.c. voltage connections of the station in question (in FIG. 12: the station, B) indicate a typical curve function from which pulse F_(ff) is derived.

FIG. 12 assumes that the line has become deactivated during a malfunction and converter 1A thus blocked or has been regulated to zero d.c. voltage α_(A) =90°. In order to recognize in the station, B, that the station, A, started normal operation, the commencement of rectifier operation is introduced by a pulsating shift of control angle α_(A) at time t₁. At time t₂ a smooth running up of the control angle to an operating value near to full-open control proceeds. This leads to the depicted pattern of U_(dA) and i_(dA) with t₂, in particular being preset so that i_(da) >0 can be maintained.

With a delay reflecting the line travel time, a typical voltage pattern U_(dB) appears in the station, B, whose differential in the station, B, monitoring device is monitored for possible exceeding of either a positive or a negative limit value. The limit value warning devices 731.1 and 731.2 designed for that purpose therefore set a flipflop 731.3 for a time period ΔT_(H) which is reset from the start of the malfunction, e.g. malfunction signal F_(dB). Circuit 731.4 monitors the time period ΔT_(H) or its significance, for example, by entering the output signal of the flipflop monitor in a shift register which generates an external release impulse F_(ff) if the output signal Φ_(D) shows the typical stored period ΔT_(H). The station, B, after a preset lag time then also resumes its normal operation by a smooth running up of the control angle α_(B) at time t'₂.

Similarly, further monitoring arrangements and logical combinations of the respective release signals or malfunction signals can be designed in order to clearly handle any special operating cases. The design and installation of such logic circuits can be additionally installed at any time by those skilled in the art using circuitry such as depicted in FIG. 11 as soon as it is detected in the course of investigating the possible operating statuses and operating malfunctions, any conceivable ambiguities in the generation of the external release signal, the external malfunction signal, the internal release signals, and the internal malfunction signal.

The particularly simple monitoring device shown in FIG. 11 can be supplemented or expanded by further monitoring elements which permit a more precise recognition of the operating status of the external station, with the information obtained from the HVDC transmission line connections regarding the operating quantities of the external station also being usable to control the former station in normal or emergency operation.

This is demonstrated in FIG. 13 for the station, A, using a HVDC transmission line whose converter, 1A and 1B are respectively connected to the HVDC transmission line using converter reactance coils and filtering circuits in accordance with FIG. 1. The HVDC transmission line voltage itself is depicted in the replacement circuit as the sequential connection of series inductances L1 through LN and parallel capacitances C0 through CN.

In the station, A, the automatic control device can be recognized by the summation point 42A and linearization device 40A, which aside from the output signal of the control variable controller 41A' to which can be connected via selector switch 61A' the fault indication voltage i.e., HVDC transmission line voltage U_(dLA) or a model value U_(dB) for the fault indication voltage to function as the automatic control voltage U_(dAv).

The computing circuit to generate the model value U_(dB) is installed here in the monitoring and programming circuitry 62A' as an additional computing component 43A" which in part also has a monitoring function, as will be explained in FIG. 14. At the same time it supplies also a model value i_(dB) for the HVDC transmission line current i_(dB) of the external station which serves as a replacement actual value for the control variable controller 41A'. The corresponding set value i*_(dB) is supplied by the run-up function generator 66A which optionally, by selector switch 60A, is connected either to the output signal of a superimposed controller 68A (e.g., for amplitude U_(A) of the a.c. voltage system, NA) designed for emergency operation, or the output signal of a superimposed controller 51 designed for normal operation. For controller 51, in particular, the same automatic control can be designed as shown in FIG. 7.

Computer component 43A" simulates the structure of the HVDC transmission line as shown, for example, in the manner of FIG. 14. For that purpose the actual value of the converter output d.c. current i_(dA) is obtained at the SRA block and supplied to the HVDC transmission line simulating circuit. The filter circuits of both stations are simulated by these circuits FA and FB.

Thereby model values i_(FA), U_(dLA), and U_(CN) =U_(dLB) for the electrical values i_(fA), U_(dLA), and U_(dLB) of the HVDC transmission line are generated using the designations of FIGS. 1 and 13. Only the converter reactance coil LB has to be simulated as the integrator from the filter circuit of the, B, which supplies, based on U_(dLB) and model value U_(dB), the model current i_(dB). To generate U_(dB), first using the subtraction point 75 one can subtract the ohmic voltage drop r_(H).i_(dA), which corresponds to the resistance r_(H) of the HVDC transmission line, from the model value U_(dLA). In addition, however, one has to consider that the external converter controls its HVDC transmission line voltage U_(dB) by drawing current from the HVDC transmission line. Said current i_(dB) is, however, determined by the current i_(dA) impressed before the HVDC transmission line travel time.

Therefore the control differential i_(dA) -i_(dB) can be eliminated by a reset controller 76 whose output signal corrects the U_(dB) and eventually ensures that the model current i_(dB) in normal operation corresponds to the actual current i_(dB) of the foreign station.

A failure of the foreign converter can be as easily recognized by the differential U_(dLA) -U_(dLA) or the control differential i_(dA) -i_(dB) at the comparison circuit 721 of the monitoring device of FIG. 11. In said malfunction the d.c. voltage U_(dB) namely is short-circuited and the HVDC transmission line discharges itself through the short circuit. Given an initially unchanged control angle α_(A) in the station in question, the current i_(dA) therefore rises following a lag determined by the HVDC transmission line travel time. As the simulation in FIG. 14 has, however, not yet taken said short circuit into account, the differential i_(dA) -i_(dB) reaches high values.

If in the model circuit of FIG. 14 following said malfunction warning, the voltage U_(dB) is now short-circuited by selector switch 77, then the malfunction situation of the short-circuited external station, i.e., inverter failure, is also simulated. In this condition the model circuit is in a position to recognize from a renewed sudden change of i_(dA) -i_(dB) when the external converter resumes its normal operation and the HVDC transmission line impresses a voltage U_(dB) not equal to zero. The selector switch 77 is then repositioned and once again the resumed normal operation is simulated.

In a model circuit in FIG. 14 one has therefore the first form of a system observer which determines simulated values for the electrical quantities of the external station exclusively from the electrical quantities available in its own station. Remote signal lines are also not required in this arrangement, and the information regarding the operating status of the external station is available following the shortest possible delay, namely the travel time of the HVDC transmission line itself.

Naturally this principle, whereby the foreign station by simulating the HVDC transmission line and several circuitry components of the external station is monitored in the station in question, can be further improved and modified if required. The advantage in this connecton is that with i_(dB) and U_(dB) model values are available for the electrical quantities of the other station, both for normal as well as malfunctioning operation.

Therefore, as already discussed, the model current i_(dB), in particular, can be used as the substituted actual value for the current controller 41A' in FIG. 13, which thereby permits control of the current flowing through the short-circuited external station in the event of a malfunction.

This principle of system monitoring also permits recognition of the end of the malfunction in a malfunction situation and, depending upon the type of malfunction, transition into normal operation with high power transmission within a few milliseconds, e.g., 10 ms approximately.

Transition to Normal Operation: Thyristor Selection and System-Synchronous Firing

In the normal operation described above the HVDC transmission line can also be used due to its capability of rapid control of power transmission to dampen balancing processes, to position the system for reactive load, and for other tasks. For that reason it is advantageous for users of such systems that following failure of the HVDC transmission line normal operation resumes as soon as possible.

In this context various types of malfunctions must be differentiated.

If in the first station operating as the rectifier, the system NA, breaks down or a converter malfunctions, then a short circuit of the d.c. voltage U_(dA) arises. If the HVDC transmission line has fully discharged during the first station's breakdown via a short circuit line or, for example, even via the converter of the second station, and if the second station is switched off to avoid an energy flow reversal, without, however, there being a malfunction either in the a.c. voltage system or in the converter in the second station, i.e., functioning station, B, then following the end of the malfunction the task is to run up the currentless HVDC transmission line from the now recuperated station, A, when the system voltage U_(A) returns.

The same task is also at hand if after initial installation or after maintenance work the HVDC transmission line is placed into operation.

The invention also deals with the case in which following a rectifier malfunctioning the HVDC transmission line has not been fully discharged. For example, the rectifier operation could have been interrupted only for a short period or the converter 1A could have been bridged by a bypass circuit without converter 1B being shut down. In this bypass operation the HVDC transmission line serves only as a reactive load for the system, NB, and remains charged. The current flowing through the bypass line functions as reactive current for the functioning station.

Such bypass operation has the advantage that the HVDC transmission line does not have to be run up from a fully discharged level, but the current rather has to be raised only to the level designed for normal energy transmission, thereby reducing the startup time. In addition, even during the malfunction, the HVDC transmission line can be used to stabilize the system in the functioning station.

The bypass circuit can thereby be closed over its own bypass switch (switch 80A in FIG. 13) of the station, A; preferrably, however, the bypass circuit is routed via thyristors lying in series of converter 1A, e.g., thyristors R⁺ ', R⁻ ', R⁺ ", R⁻ " of FIG. 1. In both instances, though U=0, the bypass circuit results in i_(dA) ≠0, U_(dLA)≠ 0, U_(dB) ≠0.

In this case, thus, one must take into account that the functioning station, B, is current-conducting and that the increasing HVDC transmission current arising during resumption of normal operation must not lead to any inverter failure in that station.

In the station, B, a drop of the a.c. voltage U_(B) results in a sudden rise of the current flowing into system, NB, with the current commutation exceeding the decisive maximum extinction angle, i.e., the protective angle, for the inverter step limit. The inverter therefore fails and short-circuits the voltage U_(dA). Here as well the design can foresee shutdown of the converter 1A of the functioning station based upon a malfunction warning so that the HVDC transmission line discharges via the short-circuited station, B.

Here as well, it is advantageous to continue operating the station, A, and recharge the HVDC transmission line with the station, B, being short-circuited by a bypass circuit. For this bypass circuit also a bypass switch (80B shown in FIG. 13) or specific thyristors preselected by programming and arranged in series in converter 1B can be used, or directly the thyristors of converter 1B which reflecting their phase position of the a.c. voltage system, NB, happen to conduct current during the malfunction and initiate the failure. Due to the already described advantages of bypass operation a bypass circuit in the station, B, itself could be desired, even if, depending upon the type of malfunction, no inverter failure arises necessarily or the operators permit a punctual shutdown of converter 1B.

Particularly in the event that the bypass circuit of station, B, is routed over the thyristors which during the failure happen to be current-conducting, the thyristors with which the system-synchronized normal operation is to be resumed have to be dealt with depending upon the system beat on the one hand, i.e., on the phase length of the returning a.c. voltage U_(B), and depending upon the thyristors already conducting current in bypass operation, on the other hand.

The required phase position for the system-synchronous startup of the a.c. voltage returning to the recuperated station can, however, initially only be incompletely detected by the reference voltage generator because this a.c. voltage usually has superimposed on it a combination of back-electromotive-force and harmonics which only decline gradually. The invention permits synchronization errors up to 30 degrees and permit resumption of normal operation in the recuperating station as early as a few milliseconds afterwards in such a fashion that the functioning station can recognize this operating condition rapidly and for its part respond by resuming normal operation as well.

For resumption of normal operation in accordance with this invention it is important that the recuperated station sends a signal over the HVDC transmission line when the malfunction is corrected that is unmistakably recognizable in the functioning station. Preferrably the recuperated station impresses a voltage pulse into the HVDC transmission line. Since, however, the impressing of a voltage pulse is particularly difficult after a malfunction in the inverter, it is desirable to initially describe the impressing of the voltage pulse in the station, B, based upon FIGS. 15 through 22, whereby the required mechanism in station, A, will be seen to be merely a simplification of the mechanism already described for the station, B.

In the left-hand portion of FIG. 15 the already known configuration of regulation and control mechanism 4B, the monitoring mechanism 64B and the memory circuit 63B are shown. As this figure refers to a converter 1B comprising component current converters in accordance with FIG. 1, the design incorporates two run-up function generators 66B' and 66B" in the run-up function generator 66B already familiar from the 4B unit in FIG. 8. These two run-up function generators can be started at different times by firing pulse release signals QIZ and can be connected to the automatic control device 42B following a time lag which can be set using a delay circuit ZS.

The monitoring device 64B is only symbolically depicted by the malfunction memory 700 and the gates 701 and 725, whereby gate 701 issues the release signal F_(fB) to the malfunction memory even in the event of a start pulse start command such as one obtained from the memory circuit 63B being inputted.

To explain the circuit, we will start with the case in which the HVDC transmission line is started up with such a start command from the de-energized condition in which all thyristors will be clamped by the clamping circuits. In the left-hand portion of FIG. 16 said clamped status is depicted. For T₀ the control angles α'_(B) ·=α_(B) "=90° are preset corresponding to the zero output voltage of the converter. The drive unit STB' then supplies, for example, a system-synchronized firing command R⁺ 'α corresponding to α_(B) =90° which along with the start command is passed to an AND gate GU1 as shown in FIG. 15, generating only at time T_(0'), an output signal FS₀. The firing command R⁺ 'α is selected from the firing command sequence S'α in accordance with the automatic programmed operation mode specified for this case because the system-synchronized firing cycle of converter 1A' is to begin with thyristors R⁺ ' and S⁻ '.

The signal FS₀ is passed through an OR gate GO1 as a synchronous startup release signal FS on the dynamic input of a dynamic flipflop IZ. There it generates the firing pulse release signal QIZ=1, whereby the run-up function generator is triggered if there is no system malfunction, e.g., if QB=0.

FIG. 16 also shows the firing commands R⁺ α' through S⁻ α' generated by the drive unit STB' for the component current converter 1B' as well as the commands R⁺ α" through S⁻ α" generated by STB" for the component current converter 1B", whereby to simplify the process it is assumed that α_(B) '=α_(B) ". These firing commands generated by the drive units are, however, inhibited before time T_(0') and thus shown only by broken lines.

This inhibiting takes place in the clamping circuits BS' BS" triggered by QIZ through AND gate GU2 as indicated in FIG. 17. By the coincidence of the start signal and the firing command R⁺ α' at AND gate GU1 finally QIZ=1 is set and the inhibiting of the firing commands removed so that now the firing commands can be passed through the corresponding amplifiers VR⁺ through VS⁻, thereby firing the thyristors R⁺ and S⁻ in the respective component current converters.

These thyristor firing proceed reliably since the signal FS₀ at the same time generates an impulse FZ₀ via a pulse generator IF₀ which via OR gates GO3R⁺ and GO3S⁻ regulates the amplifiers VR⁺ and VS⁻. This means that the firing pulse R⁺, in contrast to the firing command R⁺ α' issued by the drive unit is extended by the crosshatched surface marked in FIG. 16, while the crosshatched surfaces for the firing pulses S⁻ α', R⁺ α" and S⁻ α" show the pulses FZ₀ coupled over GO3R⁺ and GO3S⁻.

If a control angle α≦90 is preset for each relevant component current converter, then thyristors R⁺ and S⁻ fire and pull the voltage to the HVDC transmission line poles 2 and 3 (station A: U_(A) ≧0, station, B: U_(dB) ≦0 in accordance with the preset symbols) which thereupon by a change in the control angle can be run up to the operating value designed for normal operation, which in the example of FIG. 16 represents increasing the control angle to α_(B) =150° in the station, B.

This even applies if the preset control angle α in contrast to the reference voltage of the reference voltage generator due to an angle error δ_(A) <30° of the reference voltage generator in contrast to the actual phase position of the system corresponds to an actual firing angle of a maximum of 120 degrees. Only at this limit angle does the coupled system phase voltage U_(RS) which is to be coupled by R⁺,S³¹ become negative and the coupled firing pulses R⁺,S⁻ have no impact.

This does not change even if at time T'₀ the thyristor combination R⁺,R⁻ and/or S⁺,S⁻ are already current-conducting, as is foreseen, for example, for a bypass operation during a system malfunction. Since even then R⁺ and S⁻ will lead to the fact that the current commutates on the thyristor combination R⁺,S⁻.

If the bypass thyristor combination also includes the thyristors T⁺,T⁻, then the firing pulse leads to a current flowing via R⁺,T⁻, and the coupled pulse S⁻ remains similarly ineffective as does the next T⁻ pulse which normally follows in the firing cycle on the R⁺ pulse at time T_(0') in the firing pulse release signal QIZ=1. Only the subsequent firing pulse in the firing cycle, i.e., S⁺ will then bring about the normal current conductance over S⁺,T⁻. The voltage, which until then was connected to the HVDC transmission line by the commencement of the system-synchronous normal operation, thus presents a voltage pulse which corresponds to a temporary rectifier operation with U_(dA) >>0 or else U_(dB) <<0.

The circuit portion described thus far can therefore not only be used for startup of the de-energized HVDC transmission line using the start command, but also for the commencement of system-synchronized converter operation in other operating conditions. If, for example, following an internal malfunction the dynamic flipflop IZ is set to the output signal QIZ=0 over the reset input due to a corresponding output signal QB=1 of the malfunction memory 700, then the converter is inhibited. If given a longer malfunction the HVDC transmission line voltage has dissipated, then a release signal F_(fe) can now call up the signal status Qb=0 so that the dynamic flipflop IZ' can start up again with a startup command and a consequently derived pulse FS₀ =1.

With an internal malfunction it can, however, also be designed so that a bypass circuit closes when the current i_(dB) in the station, B, disspipates, in which, for example, the thyristors T⁺ and T⁻ are fired.

This thyristor firing takes place if the signal QB set by the internal malfunction is coupled to memories SBT⁻ and SBT⁺ which in this bypass thyristor combination are set to 1, using a bypass supplemental pulse BZ generated by a pulse shaper IF using the AND gates GU3T⁻ and GU3T⁺ through a firing pulse VT⁻ and VT⁺. If now the bypass operation is ended by a start command, then when the firing command R⁺ α' appears, the gate GU1 again issues a signal FS₀ which clears the firing command inhibit by the flipflop IZ in the clamping circuit BS of FIG. 17 and moreover circuits the corresponding firing pulses to VR⁺ and VS⁻ using the pulse generator IF₀.

FIG. 18 shows the pattern of the thyristor currents iR⁺ through iT⁻, whereby initially during bypass operation iT⁺ and iT⁻ flow until due to the described normal firing pulse sequence R⁺,T⁻,S⁺,R⁻ - - - initiated by FZ₀, the above-described current commutations discharge. Using as an example a non-symmetrical system with strong harmonic signals when the system resumes operation, whose pattern is shown in detail in FIG. 22. FIG. 19 displays the resulting thyristor voltages UT⁺ and US⁺ for thyristors T⁺,S⁺ and the resulting HVDC transmission line voltages and current conductance periods which are indicated by arrows. The impressed voltage pulse is shown crosshatched and the reference polarity change is negative corresponding to the transient rectifier operation of the station, B.

Should the transient voltage pulse be more pronounced, it can easily be corrected by the control angle being shifted to rectifier operation in the respective station, with this shift being prior to the running up of the control angle of FIG. 16 or being superimposed on the start of the running up.

The same applies to the regulation of the second component current converter 1B", whereby simply the use of a lag circuit ZS which through QB regulates the corresponding dynamic flipflop IZ at a certain time lag, assures that the startup of the second component current converter takes place following a certain time lag. The design of the other components marked by a double line is identical with the device described for the component current converter 1B' so that in the following discussion both component current converters will be dealt with and explained largely as one single converter.

With this variant it is assumed for transition from bypass operation to normal operation that the HVDC transmission current i_(d) had dissipated before closing the bypass circuit and that the bypass circuit was closed by a preprogrammed selection of thyristors connected in series. The memories SBT⁺ and SBT⁻ can thereby be included in the memory circuit.

In the case of inverter failures, the series thyristors are also current-conducting; however, the thyristors which form the short circuit route depends on the instantaneous phase position of the system during the failure. In order to rapidly transfer to bypass operation, these thyristors can be retained as long as their combination is established and then in accordance with this combination those thyristors are selected among the converter thyristors that are suitable for restart of normal operation.

Memories SBR⁺ through SBR⁻ depicted in FIG. 17 serve for that purpose. They are also regulated by the firing commands Sα and determine at each phase position of the system, thus at each moment within the cycle of the control command S, over which converter thyristors at that point an inverter failure could occur. This would at least be the respective thyristor group which due to the exceeding of the maximum extinction angle, in contrast to the normal commutation sequence, still carries current and the thyristor groups connected in series thereto.

FIG. 20 assumes that the internal malfunction warning pulse triggered by the failure occurs before the drive unit issues the next firing command S⁺ (time T₁,) so that lastly thyristor T⁻ was regulated with thyristor R⁺ conducting. Therefore a memory SBR⁻ which can be reset by S⁺ α is set to the value 1 using the command Tα⁻ and indicates that thyristor R⁺ is involved in the inverter short circuit. While by QIZ=0 at GU2 the regular command S⁺, generated by the drive unit is inhibited, at GU3R⁻ the bypass supplemental pulse, shown marked by crosshatching in FIG. 20, is given to thyristor R⁻ via memory SBR⁻ and the command BZ. This thyristor R⁻, along with thyristor R⁺, which is not deactivated, now brings about a safe closing of bypass route R⁺, R⁻.

If the failure arises after another firing command, then memories SBR⁺ - - - and gates GU3R⁺ - - - bring about the relevant selection, storage and regulation of the possible bypass thyristor combination. The design can, however, also foresee, particularly in the station, A, not to make the bypass thyristor selection so dependent upon the operation, but routed always to establish a preprogrammed combination, as required several or all converter thyristor groups in series, in the memory circuit and to couple them in the event of a short circuit by regulating gates GU3 or GO2.

To generate the desired voltage pulse when proceeding according to FIG. 16, it is, however, necessary to select the required initial cycle in accordance with the preset and operation-dependent bypass thyristor combination to commence the system-synchronous operation. For bypass thyristors R⁺,R⁻ the system-synchronous firing should now start by a commutation of thyristor S⁺ or S⁻ which is the function of the selector circuit, AS, of FIG. 15.

Therefore, in accordance with FIG. 21, a pulse, e.g., pulse S⁺,S⁻, is always generated in the sequence SZ from the firing pulse obtained following the interlock GO2 and issued regardless of whether the system is in normal or bypass operation which is allocated (OR gate GO4R, GO4S, GO4T) to two series thyristor with one potential thyristor forming a bypass pair. This potential bypass combination is clamped by the AND gate GU4R . . . GU4T until in the event of a malfunction using the bypass supplemental pulse BZ the bypass thyristor firing actually occurs and the bypass combination is stored in the memories SQ_(R) . . . SQ_(T) which can always be reset at the end of a malfunction by the firing pulse release signal QIZ.

While thus the memories SB_(R) ⁺ . . . SB_(T) etc. of the clamping circuits always determine the possible bypass thyristors from the firing command sequence of the drive unit and in case of malfunctions bring about their firing, the gates GO4 select from the actual firing pulses issued the possible bypass thyristors which are only stored in case of a malfunction.

Further OR gates GO5S, GO5R, GO5T unite the firing commands, e.g., for bypass combination R⁺,R⁻, thus the firing command combination S⁺,S⁻ contained in the firing sequence Sα and required always to decommutate the current from one of the selected bypass thyristors. These firing commands then, by coincidence with the stored combination determined by gates GU5S, GU5R, GU5T, lead to a synchronized signal FSα.

The OR gate GO1 then issues as the startup release signal the synchronized signal FS instead of the previously discussed start signal "start" which in flipflop IZ generates the firing pulse release signal QIZ if IZ is released after the end of the system malfunction (QB=0).

Thereby the desired startup of the system-synchronous normal operation starts by itself after the termination of the system malfunction.

To summarize, FIG. 20 thus shows the following: In normal operation signals QR⁺ through QS⁻ always indicate a thyristor which in case of a commutation malfunction could be used during the next firing as the bypass thyristor and should be fired by the bypass supplemental pulse FZ₀ in order to close the bypass. The system malfunction induces a drop in the system voltage U_(B) at time T₁ below a preset limit value which via QIZ=0 leads to the inhibiting of the normal firing command Sα or Zα and to the coupling of the crosshatched bypass supplemental pulse to R⁻. During the malfunction, therefore, only the thyristor combination R⁺,R⁻ is current-conducting and this thyristor combination is stored in the selector circuit. After the system voltage resumes, at time T₂, and the release signal occurs, also at time T₂, setting the malfunction memory to Q_(B) =1, memories SQR, SQS, SQT of the selector circuit choose a thyristor to resume normal operation and the selector circuit then generates the startup release signal if the system-synchronous converter operated by the control angle issues the firing command corresponding to this selected thyristor. The normal firing cycle is then released by the startup release signal FS commencing with the firing of this thyristor and leading to the decommutation of the current from one of the bypass thyristors.

The a.c. voltage system starts, as FIG. 20 for the phase voltage (UB)_(R) and as the voltage amplitude UB indicates, very irregularly. The malfunction memory supplies a signal QB=1 only after a certain time required by the reference voltage generator to determine a relatively reliable phase position of the system. A rapidly working reference voltage generator is described in the German patent application P No. 33 46 291.7 and assures that thereby the phased position of the system is determined down to less than a 30 degree precision level. A lag circuit contained in the pulse generator 713 in FIG. 11 can assure that the self-release pulse Ffe in the station, B, and thus the release signal and QB=1 are only generated after the minimal time required for synchronization.

FIG. 22 depicts the overlaying of the sine-shaped fundamental frequency by counter voltage and harmonic oscillations as occurs typically for returning connected phase voltages USR, UTS, URT of the a.c. voltage system. S* shows a hypothetical set of firing pulses associated with the zero degree of modulation, i.e.; control α_(B) =90, and the fundamental frequency of the recovering system.

This set S*α is hypothetical, i.e., cannot be realized since the fundamental frequency at time T₂ cannot yet be detected. Rather the reference voltage generator generates a reference voltage U_(Bsyn) associated with the similarly hypothetical firing pulse sequence S⁺ G,R⁻ G, etc. at the hypothetical control angle α_(B) =90°. This pulse sequence is also only hypothetical because in order to implement the procedure according to this invention, no constant control angle α_(B) =90° is preset. However, a comparison of both hypothetical pulses S⁺ * and S⁺ G shows that at time T₃ a reference voltage U_(Bsyn) can deviate from the (undetectable) fundamental frequency by a phase difference which can reach up to 30 degrees. Only at time T₄ (typically T₄ -T₃ =8 msec) has the reference voltage generator built up to a point that the reference voltage U_(Bsyn) is practically synchronous with the fundamental frequency of the system, which still has superimposed on it harmonic oscillations, and the equation R⁻ α*=R⁻ G applies.

In order to resume normal operation as soon as possible after the system resumes, the design does not have a provision to wait till time T₄ for the release of the firing pulse. Rather, it suffices if the synchronization error of the reference voltage is less than 30 degrees, i.e., the firing pulses are released already as early as time T₃.

FIG. 22 assumes that for the resumption of normal operation with the control angle (α_(B) =90°) (i.e., control angle at initial setting of 0 corresponding to a d.c. voltage set value U_(dB) *=0 the system can begin and run up to a maximum value α_(B) =α_(max) within approximately two system cycles which corresponds to the nominal value projected for normal operation. Consequently thyristor S⁺ is fired at time T₃ by the firing pulse S⁺ α=S⁺ G, while at approximately time T₄ the actual firing command R⁻ α, in contrast to the hypothetical command appertaining to R⁻ G, α_(B) =90° is displaced by (α_(max) -90°)/2. At time T₅, α_(max) ≐150° is attained.

Transition to Normal Operation; Presetting the Control Angle

In accordance with the previous explanations it is thus possible that after a malfunction has ended, one station issues a pulse to the HVDC transmission line, particularly a voltage pulse, which can be detected by the other side and initiates an internal release pulse whereby normal operation is resumed in that station as well. The arrangement shown in FIG. 15 as hardware, can also be partially realized in software, and incorporated with the memory circuit 63B. The memory circuit 63B basically only has to determine which mode of emergency operation, e.g., bypass operation or shutdown of the line, are to be selected for the particular malfunction in question. The methods described below for the various types of emergency operating modes for resuming normal operation will provide those skilled in the art with adequate information as to how the individual signals of the monitoring device are to be combined in the memory circuit for each individual case in order to execute the relevant startup program in conjunction with the design of the stations shown in FIGS. 8, 9, 10 and 13.

In the following discussion, that particular station whose malfunction has caused an interruption of normal operation will always be designated as "the former station." In case of a rectifier malfunction this would be the station, A, and in case of an inverter malfunction it would be the station, B. In this context, depending upon the energy flow direction chosen for normal operation, the design can foresee that the station arranged at one end of the HVDC transmission line once plays the role of station, A, and another time the role of the station, B, since the task and design of the monitoring device and the memory circuit both for rectifier as well as for inverter operation are largely the same so that both stations are designed to be as identical as possible.

After overcoming the malfunction in the former station, the corresponding monitoring station, designated as the former station monitoring unit; generates an internal release pulse which in this former station produces the release signal, described as the leading release signal, whereby the startup is initiated.

This startup is then obtained after the HVDC transmission line travel time at the d.c. voltage side connections of the latter, undisturbed, station or of the latter converter, thereby initiating in the other monitoring device an external release pulse which produces the derivative release signal.

The basic concept for startup is then that when a non-problematic or recuperated status of the previously malfunctioning former station is established, a leading release signal is generated, initiating the resumption of system-synchronous normal operation in the former station converter. In the latter station, on the other hand, the effects of this change at the d.c. voltage side connections are converted into a derivative release signal which in that station similarly initiates the system-synchronous normal operation which thus begins after the shortest possible delay upon recuperation of the former station. Remote signal lines are not required.

This assumes on the one hand that the electrical processes brought about in the former station are clearly recognized in the latter station and, on the other hand, that the processes in both stations must be coordinated with each other.

Both prerequisites are met by having the HVDC transmission line in the former station be impressed initially by a voltage surge with the control angle of the former station converter being run up in accordance with a preprogrammed run-up function approximately to the value projected for normal operation whereby, as shown in FIG. 22, the voltage surge is either necessarily generated by the run-up of the control angle or, if required by the situation, can be generated by a separate and temporary pulsating shift of the control angle. The control angle is then similarly run up in the latter station starting from an initial value of approximately zero corresponding to an angle of approximately 90 degrees in accordance with a preprogrammed run-up function to the value projected for normal operation.

Both run-up functions are coordinated with each other. Preferrably their run-up time would be approximately two a.c. voltage cycles.

During the malfunction the malfunctioning converter of the former station is either totally shut down or short-circuited using the bypass route. Thereby during emergency operation the model fault indication voltage in the automatic control device in the control channel of the former station drive unit does not have to be switched on. On the other hand, the relevant control angle at the end of the run-up cycle has to attain the control angle projected value projected for steady state operation at the end of the run-up cycle or at least attain this steady state value, if possible without substantial jumps. If therefore a smooth run-up is generated by a run-up generator at the input for the preset angle, then this preset angle which generally is generated by a superimposed control quantity controller, e.g., the current controller 41A or the extinction angle controller 41B, would have to be retracted to the extent that now the automatic control model fault indication quantity determines the control angle.

The preferred arrangement is therefore that the run-up generator 66A generating the run-up function be located, at least in the station, A, as shown in FIG. 10 at the entry to the automatic control voltage of the automatic control device in order to connect using the selector switch 61A the model fault indication quantity of the output signal of the run-up generator as a substitute value during emergency operation and the run-up cycle. Only after attaining the run-up function final value does the system switch over to the measured value U_(dLA) or the corresponding model value U_(dB), by switching the selector switch 61A. Once steady state normal operation has been resumed, then also the preset angle will be obtained from the current controller 41A as designed for normal operation, but which can be deactivated during the malfunction.

In the station, B, the model fault indication quantity serves to set the extinction angle and to maintain the inverter step limit. If during emergency operation the system dispenses with the automatic control with the corresponding automatic control angle α_(Bv), no danger arises regarding any possible inverter failure, since even in case of bypass operation the control angle is still far from the inverter step limit. This also applies, if after a rectifier malfunction, the station, A, starts to increase the current. If therefore the station, B, resumes inverter operation after a derivative release signal, then the preset run-up function in that station generates a controlled model substitute value for the model fault indication quantity which can also replace the model fault indication quantity obtained from the actual inductive d.c. voltage drop and lead to a limitation of the extinction angle. Therefore here as well the run-up generator can be arranged at the automatic control angle input of an automatic control device and be switched by the selector switch between the regulated preset model value supplied by the generator and the model fault indication quantity whose value is computed from the inductive d.c. voltage drop if or when the run-up value has approximately been obtained.

The two run-up functions thus provide substitute values for the relevant automatic control quantities. It thus seems initially necessary that both run-up functions coincide, i.e. are identical in terms of their curve and plateau level. Such rigid coordination of both run-up functions is, however, not required. For example, the run-up end value of the run-up generator of the station, A, can generally be somewhat higher and lead to a HVDC transmission current which could, with regard to the preset control angle in the run-up function of the station, B, lead to an extinction angle beyond the inverter step limit. The extinction angle control of the station, B, is, however, in a position to retract the control angle α_(B) in accordance with the inverter step limit.

For the various types of emergency operation the following possible variants resulted:

(a) Startup from a deactivated line.

In this case, after the malfunction arises, both converters are inhibited whereby the discharge of the line, e.g., during a short circuit of the voltage U_(dB), could be handled by the short circuit in the station itself or also, for example, given a rectifier malfunction in the station, A, by a forced temporary firing angle shift in the other functioning station.

When the malfunctioning system goes back on line, the corresponding internal release pulse in the former monitoring station initiates the leading release signal. The resuming normal operation in the former station initiates the derived release signal in the latter station, which there, too, initiates the startup in accordance with the preprogrammed run-up function. Both run-up functions start at an initial value of approximately zero, i.e., control angle approximately 90 degrees.

As a supplement, the design can foresee that the control angle of the former station is determined from the run-up function and a temporary additional shift in the direction of the rectifier wide-open control, wherein this additional shift can either be set before or superimposed upon the run-up function.

Given a malfunction of the inverter operation in the station, B, this means that the already described negative voltage pulse, which is impressed when resuming normal operation, is reinforced. This simplifies both the generation of the derived release pulse as well as the start of rectifier operation in the station, A. Even after a malfunction of rectifier operation in the station, A, such a pulse is advantageous since it means that current i_(dA) and voltage U_(dA) rise rapidly and charge up the HVDC transmission line so that both the run-up of the power transmission to the value projected for steady state normal operation can take place more rapidly and the derived release signal of the station, B, can be generated more easily.

(b) Emergency operation with bypass circuit.

In case of longer malfunctions the operation can proceed using the bypass circuit, whereby in the malfunctioning former station, when the internal malfunction warning pulse arises, the system-synchronous firing commands of the converter in the former station are inhibited and the bypass circuit closed. As already explained, this bypass circuit can best be closed by the firing of selected converter thyristors in series. In the latter station using the external malfunction warning pulse, the control angle is shifted to such an extent to rectifier operation as required to feed bypass current into the HVDC transmission line to meet the requirements of the latter system.

The transition from this bypass operation to normal operation takes place when the system of this former station has recuperated and generates the leading release signal which initiates resumption of system-synchronous converter operation with the control angle running up to the proper operating degree of control. Simultaneously the bypass circuit is extinguished which generally no longer requires any special measures to be taken if no specific bypass switch or bypass thyristor, but rather a series of converter thyristors required for normal operation, were being utilized.

In the latter station the derived release signal then initiates resumption of normal operation whereby the control angle runs up to the control angle steady state value in accordance with the run-up function from the control angle determined by the bypass current.

If the bypass operation resulted from a malfunction of the the station, A, then it is not necessary to undertake an internal pulse shaping displacement of the control angle at the start of the run-up cycle, and the system-synchronous firing at the start of the run-up cycle, i.e., the introduction of normal rectifier operation, poses no problems. Rather, in accordance with FIG. 16, the rectifier operation can begin with the synchronous operation of specific preprogrammed thyristors. Even the selection of the bypass thyristors is preferrably programmed whereby the bypass current can be routed not just over one bypass circuit formed by thyristors in series, but rather over several or even all the converter thyristors. This is possible and under given circumstances advantageous if, for example, suitable measures are taken in the, station, A, to ensure that after a malfunction the returning system, NA, will not immediately discharge again via the bypass circuit.

During bypass operation wherein the bypass circuit is closed by thyristors in series of the converter of the station, B, the selection of the bypass thyristors for the duration of the malfunction is stored. In accordance with this stored thyristor combination one of the thyristors is selected by the selector circuit as described in FIG. 15 for resumption of the system-synchronous normal operation. In the cycle of the system-synchronous firing commands this thyristor then corresponds to the decommutation of the current from one of the bypass thyristors.

Fluctuation Between Normal Operation and Emergency Operation

The normal operation described permits, in accordance with the automatic control principle, rapid control of the HVDC transmission line without, however, being able to exclude a malfunction altogether. The principle of programmed run-up without the use of initiating remote control signals permits transition into normal operation both given a deactivated HVDC transmission line as well as in case of bypass operation within very short startup times. The bypass operation principle described below thus permits, given a malfunction of one of the two stations, the operation of the HVDC transmission line even during the malfunction as the reactive load for the a.c. voltage system of the normally functioning station and to be regulated or controlled in accordance with the requirements of the normally operating system.

Each of these three principles: automatic control, programmed run-up, and bypass operation can, in conjunction with other operating procedures of a HVDC transmission line, be advantageously used separately or in conjunction with another one of these principles. The combination of all three principles described below permits rapid control of the HVDC transmission line, both in normal as well as in emergency operation, in order thereby, for example, to dampen sub-synchronous resonance occurances or other dynamic balancing processes in the systems, to minimize the economic effects of a malfunction, particularly of a voltage drop in one of the a.c. voltage systems and always to be able to complete the transition between normal operation, bypass operation and occasional, unavoidable operation with deactivation of the HVDC transmission line, within the shortest possible time.

The principle of bypass operation, including the transition into bypass operation in case of a malfunction, is explained in further detail based upon the signal patterns in FIGS. 26 and 27 and the design models of the two stations shown in FIGS. 9 and 10. Aside from this bypass operation it could be necessary, depending upon the type of malfunction, to deactivate the HVDC transmission line during the malfunction; this type of emergency operation is shown in FIGS. 24 and 25. To resume normal operation, it could be desirable, as already explained, both for a HVDC transmission over long distance as well as for a short coupling that, for example, the transition from bypass operation to normal operation be designed so that the malfunctioning system primarily carries reactive current when the voltage resumes.

This transition can be influenced not only by the d.c. current itself which has to be run up, but also from the number of available component current converters simultaneously participating in the transition. Thereby the possibility arises of decoupling the desired gradations in the d.c. current rise from the rise of the system reactive current in discrete steps so that thereby the requirements made of the system and of the current control can be handled separately to a certain extent in accordance with the number of separately connected component current converters.

This can be done in accordance with FIG. 15 by having the timer circuit ZS, which releases the generation of the firing pulse release signal to disable the clamping switch BS" of the component current converter IB" at the reset input of the dynamic flipflop, delay the start of the system-synchronous converter operation against the component current converter 1B'. The pulse release of the individual component current converters selected and dependent upon the combination of bypass thyristors, thus proceeds in steps including time delays, whereby the upswing of the system-reactive load also proceeds in steps.

In the following discussion, a run-up function is selected for the increase of the control angle in general which drives the control angle from a value which, if necessary, deviates slightly from 90 degrees in a linear fashion till it attains the steady state condition. Although initially it seems essential that the two run-up functions, which as regulated values substitute for the preset operating model value of the model fault indication voltage when transitioning into normal operation, be practically identical, such tight coordination of both run-up functions is not in fact required. It can in fact be advantageous to preset the two run-up functions to run in opposite directions insofar as, for example after a malfunction in the station, B, the control angle of the rectifier can be run up initially with a larger slope and later with a declining slope, while the inverter control angle initially mounts slowly and later mounts more rapidly.

Thereby the functioning station is to be recharged by active current as quickly as possible so that the HVDC transmission line can be recharged quickly. For the initially malfunctioning station whose returning voltage often displays marked switch-on peaks, the HVDC transmission line initially functions as a voltage reducing reactive load while at the same time attaining reliable commutation.

(a) Example with different run-up functions

FIG. 23 shows this run-up variant using as an example a system shortcircuit in system, NB, and a bypass operation during the malfunction.

At time t₁₀ voltage U_(B) breaks down and the limit value warning output signal G711b indicates a shortfall of the limit voltage U_(Bgrenz) and sets the controlling malfunction signal QB=0. This initiates a commutation lock in the clamping device of converter 1B, whereby all regular firing commands of the drive unit are suppressed while simultaneously the bypass circuit is fired by a supplemental bypass pulse; this condition is symbolized by a control angle α_(B) =90° in accordance with the output d.c. voltage U_(dB) =0.

Using the bypass circuit, the charge in the HVDC transmission line and the filter of the station, B, is reversed as can be recognized by a current flow i_(dB) (which often does not even attain the condition i_(dB) =0) whose extent is exaggerated in the depiction of FIG. 23, and the oscillation of voltage U_(dLB) at the end of the converter reactance coil LB facing away from the converter. The voltage U_(dB) which during normal operation, for example, was held constant at an operating value U*_(dBo) and was short-circuited during the current surge takes on a negative value, if the current i_(dB) due to the charge reversal becomes zero and the bypass thyristors extinguish. The control quantity control 41B, as shown in FIG. 9, already made line-ineffective due to the disabling of commutation and which would only display irregular values during the malfunction by a defined value Δx_(B) =0.

Similarly, switch 61B can be switched to the temporarily inactive run-up function generator 66B at the same time or after the appearance of the malfunction signal QB=0 from the circuit 43B' which computes the model fault indication quantity from actual values i_(dB) and U_(B).

The current i_(dA) of the station, A, which during normal operation is controlled to the operating set value i*_(dAo), i.e. the normal value, similarly shows, following the transmission travel time, an increase wherein the difference i*_(dA) -i_(dA) attains a limit value which leads to the derived malfunction signal QA=0 (t'₁₀). Thereby the control angle will no longer be preset in a normal fashion wherein the corresponding nominal value α*_(Ao) (e.g., α*_(Ao) ≐150°) respectively. Δx*_(A) is generated by current controller 41A, as shown in FIG. 10, adjusting the i*_(dAo) parameter and whereby the fault indication voltage U_(dAv) is generated by a measurement circuit as the automatic control quantity U_(dAv). Rather by reversing the switch 60A at time t₁₀ the system switches from the set value for the operating current to a new set value supplied by a bypass controller, i.e., a controller for the voltage U'_(A).

As in the case under consideration only a bridging circuit of converter thyristor groups in series was selected and fired as the bypass circuit and as this bridging circuit has to be capable of bearing permanent current, its thermal load bearing capability is lower than for normal system-synchronous operation. Therefore the bypass current set value supplied by the bypass controller is throttled back in contrast to the nominal value i*_(dAo).

The control angle supplied largely by the bypass controller 68A is symbolically assumed to be a constant in FIG. 23. Until the end of the bypass operation it can be pre-regulated by the measured voltage U_(dLA) or even by the substitute U_(dLA) or U_(dB) generated according to FIG. 14; according to FIG. 23, at time t'₁₂ the automatic control is switched onto the initially inactive run-up generator 66A in order to prepare for a normal start.

The d.c. current i_(dbypass) now supplied by the functioning the station, A, flows, after the voltage U_(dB) passes to the zero point at time t₁₁, over the bypass thyristors until voltage U_(B) returns at time t₂₀ possibly with substantial voltage spikes.

The limit value warning signal G711B supplies at a delay T_(syn) in accordance with the synchronizing time of the reference voltage generator the leading release signal QB=1 used to start the component current converter 1B' with control angle α_(B) '≐90°, whereby the component current converter 1B' is shifted at a low increment of, for example, 10 degrees into converter operation. Following a delay T_(ZS) supplied by the timer circuit ZS, as shown in FIG. 15, the component current converter 1B" is also released.

Thereby initially, as already discussed, a negative voltage time waveform arises in U_(dB) and the system, NB, is charged with reactive current which leads to the desired voltage decline and a reduction of voltage spikes in U_(B).

As the component current converter is switched on after a delay, the reactive load also rises in steps. Preferrably the control angle α'_(B) of the component current converter started first is left in the area near 90 degrees by having the HVDC transmission current function primarily as a reactive load, and is run up to the operating inverter degree modulation only after all the other component current converters commute fully. Thereby, as FIG. 15 indicates, a distinct run-up function can be selected for each component current converter. According to FIG. 23, however, one single run-up function generator usually suffices for α_(B), whereby the slope of α' initially impacts only on 1B' and starts at a low increment to continue at a higher increment to the nominal value α_(Bo) only after time t₂₀ +T_(ZS) after the last component current converter is started with α_(Bo) =α_(B).

The voltage pulses impressed by the station, B, lead following the transmission line travel time Tts to a motion of U_(dA), in other words, U_(dLA) ; and i_(dA), in other words, i_(dLA), which is detected in the station, A, and initiates the derived release signal QA=1 at t'₂₀. There the control angle α_(A) is run up to α_(A) ≐0, with the increment initially being preferrably large and later being throttled down. Since initially only the fault voltage U_(dB), in other words U_(dLA), impressed by the initially slight increment of α_(B) impacts on the station, A, i_(dA) rises rapidly to the nominal value i_(dAo), and converter 1A is soon in a range in which the current i_(dA) loading the system, NA, is primarily active current.

During run-up switch 60A is reversed to the operating set value i*_(dA), whereby the bypass controller is out of action. After the run-up function starts in FIG. 23 at time t₂₁ the control quantity controller 41B is activated and approximately at the end of the run-up function, at the present times t₂₂, t'₂₂ controlled by the lag circuit VZ, the operating automatic control signal is always connected so that normal operation can resume.

In normal operation thus both stations are released by the release signal QA=1, QB=1, while switch 61A and 61B are always positioned by the last firing pulse release signal QIZ=1 so that the control angles α_(A) and α_(B) are determined in the automatic control device by the addition of the projected model fault indication quantity and the respective preset angle, i.e., the angles determined by the quantities Δx_(B) and Δx_(A) shown in FIGS. 9 and 10, for normal operation. Similarly, reversing switches 60A and 60B are held in a position whereby the preset angle α_(A) *, and respectively, γ_(B) * is determined by the control quantity control projected for normal operation. For example, in accordance with FIG. 7, to generate X_(A), the set value i*_(dA) of the current controller 41A in the station, A, is supplied by a superimposed controller such as active power controller 51, shown in FIG. 7, in accordance with the active power balance or other requirements of the undisturbed system, NA. In the station, B, Δ X_(B) is supplied in accordance with a set value, γ*, supplied either by an extinction angle controller, such as 41B of FIG. 5, a reactive current controller, 41B', or voltage regulator, 41B", with γ* derivable in the computer circuit 47 from the system requirement for reactive current or constant voltage.

Since for maintenance on the HVDC transmission line itself it might be necessary following a malfunction to deactivate the HVDC transmission line in terms of current and voltage, i.e., not undertaking any bypass operation, this situation will be considered first.

(b) Examples with Transmission Line Deactivated

In a typical sequence as shown by FIG. 24 the case in which the former station, B, at time T₁₀ faces a short circuit of system, NB, i.e., a breakdown of voltage U_(B), is considered first. In the monitoring station the limit value alarm 711 issues the corresponding signal G711B. The HVDC transmission line, the converter reactance coil, LB, as well as the filter elements CFB and LFB discharge via the short circuit so that the currents i_(dB), in other words, i_(dLB), initially rise, leading to an inverter failure. At the same time, the malfunction signal QB=0 is set and the firing pulses of converter 1B are inhibited as indicated in FIG. 24 by the control angle: α_(B) =90°.

Thereby the voltage U_(dB) drops and the HVDC transmission line current extinguishes.

In the station, A, following the travel time Tts determined by the HVDC transmission line flow time there is a similar increase in the HVDC transmission line current i_(dA), in other words i_(dLA), which over the external malfunction warning pulse produces a malfunction signal and leads to QA=0 at time t_(10'). Thereby this other station, A, is also shut down: α_(A) =90.

FIG. 24 assumes that due to a short circuit on the side of the station, B, the HVDC transmission line has been practically completely discharged with the exception of slight oscillations in the HVDC transmission line, which is now locked on both sides. In this context it can be of particular advantage if with QA=0 the other converter 1A is not immediately locked, but rather the HVDC transmission line current and voltage dissipate fully down to the value zero over the controller of the station, A. Such a procedure is particularly advantageous if, for example, following a short-term interruption the HVDC transmission line is to be started up as rapidly as possible from the deactivated position.

In this restart, as soon as the voltage U_(B) has attained a specific limit value, i.e., time point t₂₀, and the limit value alarm 711 has activated in the one station following a certain lag time T_(syn) which is necessary to synchronize the reference voltage generator as well as to generate the firing pulse release signal QIZ, the run-up function generator 66B is activated and the control angle α_(B) run up smoothly.

In order to then impress the HVDC transmission line with a defined voltage pulse which can release an external release pulse in the other station, A, it is preferrably foreseen to add an additional pulse Δα to the smooth run-up of the control angle α_(B) or to overlap said pulse, by means of which the converter 1B is temporarily operated in rectifier operation. FIG. 24 shows that the HVDC transmission line current i_(dB) is thus rapidly excited and the HVDC transmission line voltage U_(dB) becomes temporarily negative.

As a consequence, again at time t₂₀ determined by the HVDC transmission line travel time, a negative voltage vs. time waveform in the thus far locked station, A, and a signal QA=1 result, with which the run-up function generator inactivated during malfunction is activated there and the control angle α_(A) is run up smoothly.

In both stations during the malfunction inactivated run-up function generators supply during the run-up initially a substitute value for the model fault quantity, although one can recognize from the pattern of the control angles α_(A) and α_(B) that the smooth preset value supplied by the run-up function during the run-up is replaced by the pulsating model fault quantity as soon as the reversing switches 61A and 61B and also switches 60A and 60B are reversed and the undisrupted normal operation is resumed.

FIG. 25 depicts the case of a malfunction in the station, A. This assumes that in the system, NA, at the time t₁₀ only one of the phase voltages fails so that the voltage amplitude U_(A) of this system shows a pulsating pattern. In this case the limit value alarm 711 also supplies a pulsating signal to one monitoring device which, however, is only shown by the broken line in FIG. 25 because, for example, the time constant of pulse shaper 713 can be set so that a constant signal suppressing these oscillations can be generated. In the case already mentioned, wherein no specific limit value alarm is designed to form the signal G711B, but the pulse generation is rather handled by the reference voltage generator which handles all the fluctuations of the a.c. voltage system anyway, the relevant constant signal for the total extent of the malfunction can be generated there easily.

In general, for such a malfunction another type of emergency operation is designed which is not the subject of this invention. The strategy designed for a malfunction of the rectifier with deactiviation of the HVDC transmission line will be explained, however, for this case as well.

The inhibiting of the firing pulses of converter 1A generated by QA=0 brings about the extinction of the HVDC current i_(dA), although admittedly there is no necessary immediate discharge of the HVDC transmission line. Such a discharge can be forced, as already explained in connection with FIG. 24, by a temporary firing angle shift in the undisturbed other station, B, which, however, is dispensed with in the example of FIG. 25. Rather, the firing pulses of converter 1B in the station, B, are inhibited following the lag time Tts by the collapsing HVDC transmission line current i_(dB) or HVDC transmission line voltage U_(dB) so that there, too, the current is discharged and the converter shut down. The HVDC transmission line then no longer conveys current, but still conveys voltage.

In such a case it is often not necessary following the return of the system, NA, i.e., time T₂₀, to begin the transition to normal operation with a temporary supplemental pulse Δα on the control angle. This applies, in particular, if the HVDC transmission line still retains a positive residual voltage as shown in FIG. 25, which when firing the thyristors in 1B, generates a current flow. The control angle can then be run up smoothly from approximately α_(A) =90°.

In the situations of FIGS. 24 and 25 the design foresees in case of emergency operation during a malfunction a shutdown or deactivation of the HVDC transmission line at least to the extent that the HVDC transmission line current is equal to zero which is attained by having the HVDC transmission line separated from the a.c. voltage systems by a lock of both converters during the malfunction, i.e., before the resumption of normal operation.

The subsequent transition to normal operation is thus also suitable for the initial startup of the HVDC transmission line following installation or after a thorough maintenance.

The HVDC transmission line voltage at time t₂₀ rapidly changed by the resumption of normal operation is detected at the latter station, B, at time point t'₂₀, where it leads to the derived release signal QB=1 and similarly to the resumption of normal operation.

During a malfunction the switches 60, 61 and 67 of the stations in FIGS. 9 and 10 are in a position at which the deactivated controller 41 and the run-up function generator 66 set the control angle 90 degrees in accordance with the initial setting step of zero. The control angle is run up at time point t₂₀, in other words, t'₂₀ by activating the run-up function generator, whereby position P3 of switch 61 permits temporary connection of the supplemental pulse Δα during the system-synchronous start of the drive unit. If the controllers 41 are activated simultaneously with the run-up function generators 66, then the run-up is superimposed by the buildup of oscillations of the controller, while at time points t₂₁ and t'₂₁ it can be seen from the wave pattern of the automatic control voltage that now the control angle is being determined by the automatic control quantities U_(dLA), in other words, α_(BV) which as the measurement value of the fault quantity replaces the model value generated and regulated by the run-up function generator.

(c) Examples with Bypass Operation

If, in the event of a malfunction in the former station, given undisturbed operation of the latter station, a bypass operation is specified due to the already mentioned advantages, then in the undisturbed station upon commencement of the malfunction the bypass thyristors selected for the bypass circuit are fired by the internal malfunction warning pulse, and the HVDC transmission line connections of this station are short-circuited. In the latter station the external malfunction warning pulse Fdf initiates a rectifier activity in this type of operation whereby any desired bypass current is supplied into the HVDC transmission line. This bypass current is preferrably derived in accordance with the requirements of the latter station, i.e., based upon the measured values of the a.c. voltage system available in that station.

After the malfunction is over, the bypass circuit is interrupted again in the recuperated station by means of the internal release pulse Ffe and normal operation synchronous with the system resumed, resulting in the functioning other station in an external release pulse Fff by which the bypass current feed is discontinued and normal operation synchronous with the system resumes. FIGS. 26 and 27 depict advantageous types of designs of said malfunction operation with bypass current.

FIG. 26 assumes a malfunction of the rectifier operation for example, in the station, A.

The collapsing voltage U_(A) of the system, NA, collapsing at time t₁₀ is again recorded in the station, A, by the internal malfunction warning pulse Fde and releases QA=0. Converter 1 is inhibited. The current i_(dA) thus goes off, and the voltages U_(dA) and U_(dLA), respectively are caused to oscillate. Said oscillation is depicted by a broken line and is dependent on the further events in the station, B.

After a delay time T_(ts), i.e., time T'₁₀, there is a corresponding drop in voltage U_(dB), in other words, U_(dLB) and in current i_(dB) at the d.c. connections of station, B. Therefore, by monitoring the current i_(dB), for example, an external malfunction warning pulse Fdf is generated at said location, resulting in Q_(B) =0.

If in the event of said malfunction, bypass operation is foreseen, then the functioning station, B, assumes rectifier operation with the external malfunction warning pulse, with the control angle being provided by a superimposed controller. If, for instance, the bypass operation is to serve to keep the voltage U_(B) constant or to control the reactive load, then a voltage regulator or a reactive power controller is provided as a superimposed regulator for the bypass operation. The output signal of this bypass controller 68B, as shown in FIG. 9, forms value ΔX_(B), which corresponds to the set value i*_(dB) for the current to be taken from the functioning system and is connected with the control set as control angle α_(B) in the bypass operation via the switch 60B. The computing circuit 43B' is separated in this instance, e.g., by the switch 61B being switched to the output of the run-up function generator 66B which is inactivated during the malfunction.

In one configuration, at QB=0 at the point in time t'₁₀ first the firing commands of the converter are inhibited. It then depends on the phase position of the system, NB, if and when current i_(dB) extinguishes. Subsequently, rectifier operation is commenced in the station, B, which results in a voltage reversal in the HVDC transmission line in accordance with the polarity of the converter thyristors.

The time t'₁₁ for commencing this rectifier operation (possibly with the pulse Δα being given) is practically freely selectable. The automatic control angle α_(Bv) is switched over to the run-up function generator, which is inactivated during the malfunction, so that the control angle α_(B) is determined solely by the bypass controller which has now been switched on.

The bypass operation now taken up by the station, B, has the effect that an increase in the voltage U_(dA) occurs at the d.c. connections in the malfunctioning the station, A, at time t₁₁, with the storage circuit 63A being able to recognize the bypass operation taken up by the functioning station by means of the simultaneous occurence of signal G711A and the internal malfunction warning pulse Fde, respectively, and the external release signal Fff derived from the voltage oscillation. As i_(dA) =0 at this time, it does not matter which converter thyristors of the station, A, connected in series are fired as the bypass circuit. Several parallel bypasses can be closed, for example. In the case at hand a selection of those bypass thyristors serving as bypass thyristors among the thyristors of converter 1A required for normal operation is pre-programmed and only a single bypass is foreseen.

The firing commands for this bypass circuit can be formed upon occurrence of the internal malfunction warning pulse or shortly thereafter; firing is, however, not effected until the voltage U_(dA) due to the voltage impression by the bypass rectifier operation of the station, B, has changed polarity. Then a current i_(dA) flows through the converter 1A and the HVDC transmission line, which, however, is separated from the malfunctioning network, NA.

The network, NA, resuming operation at time t₂₀ reaches at t₂₁ the preset limit value at which the internal release pulse is formed. After the time T_(syn) required for the formation of the system-synchronous reference voltage of the drive unit, the malfunction memory QA=1, and the converter 1A is run up with the control angle α_(A) in a smooth fashion.

In order to avoid a short-circuit current to flow through converter 1B, which in bypass operation initially still operates as a rectifier, and converter 1A, which has already gone to normal rectifier operation, the run-up of the control angle α_(A) can be delayed as against an initially impressed voltage surge so that the station, B, can make the transition to inverter operation in a timely manner after recognition of this voltage surge.

Furthermore, at time t₂₀ the switch 61A is switched in such a manner that the run-up function generator output signal forms the automatic control signal U_(dAv). As this run-up generator is inactivated during the malfunction and not released again until the system resumes, the depicted pattern results for the voltage U_(dAv), with a smooth increase upon occurrence of the leading release signal QA=1.

At a time t₂₂ allowed by the program circuit the voltage U_(dLA) is again used as automatic control voltage by switching switch 61A. Therefore during normal operation the control angle α_(A) is practically given by U_(dAv) =U_(dLA), or as the case may be U_(dLB), and is modified only slightly by the function of the current regulator. As the clamping circuit inhibits the firing commands of the drive unit STA derived from α_(A) during bypass operation, it is insignificant when in the interval between t₁₀ and t₂₀ the memory circuit switches from U_(dAv) =U_(dLA) to the automatic control voltage supplied by the run-up function generator. Preferrably the current controller is inactive during this time and is not activated until after the return of the system via the program circuit, preferrably at the end of the smooth run-up or upon occurrence at time t₂₁ of the effects of the normal operation initiated by the other station.

In the station, B, the rectifier operation resumed by the station, A, in a smooth manner effects at t'₂₀ an increase in the voltage U_(dB), or as the case may be U_(dLB), and in the current i_(dB), thus triggering the release signal QB=1 derived here, with which the system is now switched from bypass current control to normal control, i.e., from bypass controller 68B to the extinction angle controller 41B in FIG. 9 by switch 60B. At the same time the run-up function generator is activated there with said external release signal of the station, B, which now supplies the automatic control angle α_(Bv) for the station, B, instead of element 43B'. As a consequence, the control angle α_(B) increases again in a smooth manner to the angle characteristic of normal inverter operation until at time t'₂₂ the switch 61B is again switched from the run-up function generator to the computing circuit 43B'.

The same principle can be implemented if the station, B, has a malfunction. FIG. 27 assumes this case.

In normal operation the converter 1B in the station, B, is operated as an inverter with a control angle α_(B) near the inverter step limit, which is formed by the extinction angle controller, a controller for the reactive power or another control quantity or the case may be, and is controlled with the automatic control angle calculated from the inductive voltage drop. At time t₁₀ the voltage U_(B) of the system, NB, collapses with the effect that via a corresponding signal G711B in the monitoring device of the station, B, the normal firing pulses are inhibited there.

This short circuit also results in the collapse of the d.c. voltage U_(dB) and a rapidly increasing direct current i_(dB) flowing into the short circuit so that the inverter 1B becomes unstable. The capacitance of the HVDC transmission line at the station, B, connection are thus discharged into the short circuit, resulting in a reversal of the voltage U_(dLB) and finally in an extinction of the direct current i_(dB). Meanwhile the limit value warning device has also effected condition QB=0 via the internal malfunction warning pulse, by which the normal commutation of the converter 1B is inhibited and the firing of the bypass thyristors initiated.

According to the line's distributed time delay, the d.c. current i_(dA) increases in the station, A, and the d.c. voltages U_(dA) and U_(dLA) drop accordingly. Via the external malfunction warning pulse of the station, A, this results in condition QA=0 at which the operational current set value i*_(dA) is switched to a lower set value which is supplied by a superimposed bypass controller, e.g., the receive power controller 68A or a voltage regulator for voltage U_(A) (switch 60A in FIG. 10). The converter 1A therefore feeds only the reactive current into the HVDC transmission line which is required for as continuous an operation as possible of network, NA. Furthermore, the signal QA=0 triggers the switching of the automatic control voltage U_(dAv) from the measuring value output for U_(dLA) to the output of the run-up function generator by switch 61A switching at a preset later time t₁₂, for example.

As the station, A, continues to feed current into the HVDC transmission line, the end of said transmission line discharged through the system short circuit is recharged in the station, B. Thus the voltage U_(dA) acquires positive values again i.e., at time t₁₂, so that upon attaining a preset positive limit value, certain thyristors fire in the station, B, which are selected for the formation of the bypass circuit and at which corresponding firing voltages arise at time t₁₂. Thus the bypass circuit is now closed and the bypass operation initiated during which the HVDC transmission line is operated as reactive impedance for the system, NA.

In the case depicted by FIG. 27 the inhibiting of the normal firing commands supplied by the drive unit took place at the time t₁₀ in the malfunctioning station, B, with QB=0, whereby the current i_(dB) initially continues to flow through the thyristors of converter 1B involved in the shutdown of converter 1B. Only after extinction of these thyristors the HVDC transmission line has been recharged with a current which at time t₁₂ leads to a positive response value of U_(dB), while the station, A, has started the bypass operation, is the voltage applied to the thyristors selected for bypass operation, which voltage results in the firing of the bypass thyristors and thus in a recurring current i_(dB). In this event the bypass thyristors can be selected independent of the thyristors involved in the inverter shutdown. However, as in the station, B, the thyristors involved in the shutdown can be selected as bypass thyristors independent of operation, a frequently undesirable complete extinction of the current i_(dB) must not be waited for.

Particularly in the case depicted in FIG. 27 substantial negative values of U_(dB) can result in the time interval between t₁₀ and t₁₂, which the users try to prevent in many cases when operating a HVDC transmission line.

This can be achieved if the control angle α_(A) of station, A, is not immediately reduced to a value near zero corresponding to the bypass operation when the derived malfunction signal QA=0, but rather to a control angle which is initially shifted in the direction of a rectifier wide-open setting in order to recharge the HVDC transmission line as quickly as possible. This value can be given by the storage circuit 63A via the position P3 of switch 61A according to FIG. 10. If a network monitor 43A' is available, however, as explained in FIGS. 13 and 14, it is then possible to keep the current i_(dB) almost constant, by controlling the substitute actual value i_(dB) of the current regulator 41A' calculated by the network monitor to a set value supplied by the voltage regulator 68A serving to maintain a constant voltage U_(A). If for normal operation, for example, a superimposed active power regulator 51 is provided, then through QA=0 this superimposed regulator is switched to a bypass controller, such as voltage regulator 68A, while in the observer station the inverter shutdown of the malfunctioning station, B, is simulated by the closing of switch 77.

In order to convert from the bypass operation back to the system-synchronous normal operation upon the return of the network, NB, at time t₂₀ as shown in FIG. 7 and upon occurrence of the leading release signal QB=1, those thyristors are fired in the already described manner which have been pre-programmed with a pre-programmed bypass thyristor combination in order to initiate the system-synchronous operation while impressing a voltage surge, or those thyristors are fired which have been selected by the selector switch dependent on the operation, in accordance with the bypass thyristors fired dependent of operation.

FIG. 27 depicts the voltage U_(dB) occurring after the time T_(syn) required for synchronization of the reference voltage generator, which voltage is a function of the run-up of α_(B). At the time t'₂₀ then the release signal QA=1 occurs, with a corresponding increase of the angle α_(A) to the rectifier wide-open setting provided for normal operation and a corresponding pattern of voltage U_(dA), with the bypass control now discontinued in the functioning station, A, and normal control being switched on via the current controller. At times t₂₂ and t'₂₂ switching from the automatic control value preset as a controlled run-up function to the measured fault quantity as a automatic control quantity takes place.

In this design the particular advantage is that during normal operation the two stations function independent of one another, i.e., that no information to be transmitted via remote control lines is required from the respective other station for the control of the two converters. Therefore both converters can be quickly controlled by corresponding automatic control without forcing a slow control pattern due to the delay time of remote control signal transmission. Even in the event of malfunction the transmission of corresponding malfunction signals is not effected via remote control lines, but via the HVDC transmission line itself so that in the event of a malfunction in the one station the necessary information on the malfunction is available in the other station as well within the shortest time possible. The resumption of the fault-free normal operation in the one station is communicated in the same way within the shortest possible time so that very short on-control times result for the resumption of normal operation. Furthermore, it is possible by said rapid control to utilize the HVDC transmission line itself to control or regulate the electrical quantities of the respective systems, e.g., for reactive current control; or during bypass operation to maintain a fault-free system constant, or to dampen other processes, e.g., balancing processes in the systems.

As will be evident from the foregoing description, certain aspects of the invention are not limited to the particular details of the examples illustrated, and it is therefore contemplated that other modifications or applications will occur to those skilled in the art. It is accordingly intended that the claims shall cover all such modifications and applications as do not depart from the true spirit and script of the invention. 

What is claimed as new and desired to be secured by Letters Patent of the United States is:
 1. A method to control or regulate a system synchronous converter during normal operation of a HVDC transmission system having: a first station connected to a first a.c. voltage system; a first converter, connected to the first station, operating as a rectifier impressing a HVDC current into one end of the HVDC transmission system; and a second converter, connected to the second station, operating as an inverter drawing a HVDC current from the other end of the HVDC transmission system and delivering power into the second a.c. voltage system, thereby determining the HVDC voltage; comprising the steps of:generating a model fault indication quantity in the second station from the HVDC current and the second a.c. system voltage said model quantity encompassing the d.c. inductive voltage drop and determining an automatic control angle; generating by a control or regulating procedure a control signal determining a preset control angle generating a control voltage determining a control angle for said system synchronous converter by composing said control signal and said model fault indicative quantity, said control angle being the sum of said preset angle and said automatic control angle; and controlling the firing pulses of said system synchronous converter by said control voltage.
 2. A method according to claim 1, adapted for controlling or regulating the first converter in a HVDC transmission system containing a reactance coil between the converters, particularly in a short coupling HVDC transmission system, whereby:said model fault indication quantity in the second station operates as a substitute actual value for the d.c. voltage at the end of the reactance coil pointing towards the second converter for generating the control voltage for the first converter; said model fault indicating quantity being calculated taking into account an angle value of the second converter such as the actual value or a set value for the control angle or the extinction angle and a simulated transmitted function.
 3. A method according to claim 2, further comprising the step of: having the preset control angle of the first converter generated by a control quantity controller, such as a current regulator.
 4. A method according to claim 3, further comprising the step of: having the set value for said current regulator be composed by the output signal of an active regulator and an automatic current control quantity, said automatic current control quantity generated by the active power set quantity and said model fault indication quantity.
 5. A method in accordance with claim 1, adapted for controlling or regulating the second converter, further comprising the steps of:deriving the control signal in the second station from a control quantity for the operation of said second converter, said control quantity defining an extinction angle set value, γ*, according to a programmed function of the control quantity; and generating said model fault indication quantity according to an automatic control angle:

    αBV=180°-γ*-u;

wherein u is an overlap angle corresponding to said extinction angle set value γ* and the d.c. inductive voltage drop; said d.c. induction voltage drop being precalculation from measured actual electrical values of said second converter.
 6. A method according to claim 5, further comprising the steps of:generating a firing command for the second converter at a phase position, φ(t), of a system synchronous reference voltage according to the equation

    ΔX.sub.B +α.sub.Bv -φ(t)=0

wherein: α_(Bv) is according to the equation:

    U.sub.B cos α.sub.Bv =-U.sub.B cos γ*-2dX.sub.B ·i.sub.dB ;

wherein -U_(B) is a value proportional to the instantaneous system voltage amplitude representing the ideal no-load voltage of the second a.c. system voltage; i_(dB) is the instantaneous value of the current flowing through the second converter; d_(XB) is a parameter for the inductive voltage drop of the second converter; and ΔX_(B) is a corrective quantity determining the preset control angle; said corrective quantity being generated by a control quantity regulator in case of control quantity regulation or being calculated from a control quantity set value and the programmed function for the extinction angle set value, γ*.
 7. A method according to claim 5, further comprising the step of:determining a parameter corrective value based upon the deviation of the actual extinction angle, γ, from the extinction angle set value, γ*, used in precalculating the inductive voltage drop whereby the precalculation of the next inductive voltage drop is corrected.
 8. A method according to claim 5, wherein the generating of said model fault indication quantity occurs during a millisecond frequency of a microcomputer.
 9. A method according to claim 5, further comprising, as a supplement to said controlling or regulating the second converter in the second station, the steps of:generating a further control signal for the first converter, from the control deviation of a measured or computational model calculated value of the impressed HVDC current and a corresponding set value; said further control signal determining a further preset control angle measuring the actual HVDC voltage at the end of a reactor coil connecting to and facing away from the first converter or calculating a substitute actual value, said measured or calculated value defining a further fault indication quantity and a corresponding further automatic control angle; generating a further control voltage by composing said further control signal and said further fault indication quantity, said control voltage determining a control angle for the first converter and controlling the firing pulses of said first converter, wherein said control angle equals the sum of said further preset control angle and said further automatic control angle.
 10. A method according to claim 9, wherein said preset angles and said automatic control angles are determined in each respective station from actual and set values without the use of remote control lines.
 11. A method according to claim 9, further comprising the step of:generating said control signal of the first converter by stabilizing the control deviation, whereby, the time constant of the control process and the time constants for the control quantity of the second station, are optimized independently of the time constants of the HVDC transmission line and of the other station.
 12. A method in accordance with claim 9, further comprising the steps of:providing a reference value for a higher order controller, such as an active power controller or a reactive power controller; generating a regulating current value, from the reference value of said higher order controller and from a measured value of the HVDC voltage; and generating the reference value for the current regulator by adding said regulating current value and the output signal of said controller.
 13. A method according to claim 9, for resuming normal operation subsequent to a disruption of normal operation, further comprising the steps of:conducting bypass current during a malfunction in one of the stations by using selected thyristors to function as bypass thyristors in series with said bypass current; sustaining said bypass current by the functioning station using a single control angle which corresponds to rectifier operation with a practically short-circuited fault indication quantity; generating, in the malfunctioning station, a reference voltage; synchronizing said reference voltage to the a.c. system voltage of the malfunctioning station; providing in the malfunctioning station a control angle for the start of the normal operation; generating in the malfunctioning station, from said reference voltage and said provided control angle, system-synchronous firing commands to start normal operation; forming a controlling release signal if the synchronization error of less than 30 degrees relative to the a.c. system voltage connected to the malfunctioning station; releasing said firing commands by said controlling release signal, commutating in the malfunctioning station said bypass current, sustained by the functioning station, from the bypass thyristors to selected thyristors for resuming normal operation by the release of the firing commands; continuing the bypass current in the continuously functioning station until commencement of current commutation in the previously malfunctioning station releases in the continuously functioning station a derived release signal; and generating in each station, a startup function, replacing the respective fault indication quantity affecting the station's respective converter operation following the respective release signal in each station, and initially without knowledge of the actual control angle of the other station.
 14. A method according to claim 13, wherein the period of each said start-up function is approximately two a.c. voltage periods.
 15. A method according to claim 13, wherein the start-up function of each station starts with said control angle approximately at 90 degrees and the start-up function of at least one converter, specially of the second converter following a malfunction of the second station, can be superimposed with an addition shift, in the direction of the rectifier operation.
 16. A method according to claim 9, for resuming normal operation following a breakdown of normal operation, further comprising the steps of:inhibiting, during malfunction in the malfunctioning station, the converter thyristor of said station; de-energizing the HVDC transmission line in the functioning station by blocking the thyristors therein; resuming normal operation in the previously malfunctioning station by a leading release signal being generated therein; impressing a voltage surge as a result of said leading release signal onto the HVDC transmission line; generating as a result of said voltage surge, a derivative release signal in the continuously functioning station; initiating normal operation in said continuously functioning station as a result of said derivative release signal; generating in each station, after the occurrence of the respective release signal, initially without knowledge of the other station's actual control angle, a run-up function said run-up function replacing said fault indication quantity; whereby the run-up function in each station is coordinated to the other station's run-up function and opens each station's own control angle to the specified final setting prevailing under normal operation.
 17. A method according to claim 16, wherein the run-up function of each station starts with said control angle approximately at 90 degrees and the run-up function of at least one converter, especially of the second converter following a malfunction of the second station, can be superimposed with an addition shift in the direction of the recitifier operation.
 18. A method according to claim 16, wherein the period of each said run-up function is approximately two a.c. voltage periods.
 19. A method in accordance with claim 9, further comprising the step ofproviding a reference value for a higher order controller, such as an active power controller or a reactive power controller; generating a regulating current value, from the reference value of said higher order controller and from a computed model value, of the HVDC voltage; and generating the reference value for the current regulator by adding said regulating current value and the output signal of said controller.
 20. A method according to claim 9, for resuming normal operation following a breakdown of normal operation, further comprising the steps of:inhibiting, during malfunction in the malfunctioning station, the converter thyristor of said station; de-energizing the HVDC transmission line in the functioning station by controlling the HVDC voltage; resuming normal operation in the previously malfunctioning station by a leading release signal being generated therein; impressing a voltage surge as a result of said leading release signal onto the HVDC transmission line; generating as a result of said voltage surge, a derivative release signal in the continuously functioning station; initiating normal operation in said continuously functioning station as a result of said derivative release signal; generating in each station, after the occurrence of the respective release signal, initially without knowledge of the other station's actual control angle, a run-up function said run-up function replacing said fault indication quantity; whereby the run-up function in each station is coordinated to the other station's run-up function and opens each station's own control angle to the specified final setting prevailing under normal operation.
 21. An apparatus for controlling or regulating current transmittal by a High Voltage Direct Current system, having a first converter connected in a first station to a first A.C. voltage system operating under normal conditions as a rectifier, and a second converter connected in a second station to a second A.C. voltage system operating under normal conditions as an inverter supplying current to the second a.c. voltage system, comprising:a control or regulating device in each station, each having an output signal, system-synchronous reference voltage means connected in each station; a control circuit in each station connected to the respective control or regulating device and the respective reference voltage device and determining a control angle relative to the respective reference voltage; a first computing circuit, generating from the HVDC current and the second a.c. system voltage in the second station, a first fault indication quantity, incorporating the inductive d.c. voltage drop of the second converter; and a first automatic control unit in one of the stations adding said output signal of the respective control or regulating device with a first automatic control quantity, derived from said first fault indication quantity, said automatic control unit defining thereby said control angle of the respective converter as the sum of a preset angle being determined by said output signal and of a control angle being determined by said automatic control quantity.
 22. An apparatus according to claim 21, whereby:said computing circuit, out of an ideal no-load voltage proportional to the measured second a.c. system voltage amplitude; the measured value of the HVDC current; and a converter parameter of the second converter defining the inductive d.c. voltage drop, generating said first model fault indication quantity using said control angle or the extinction angle of the second converter; a dynamic element in series with said computing circuit such as a time delaying element of high degree; and the automatic control device incorporating a summing point element connected to said computing circuit and to said control or regulating device of the first station, said element determining thereby said control angle, α_(A), of the first converter from a model fault indication quantity, U_(dB), being defined by said computing circuit; from a measured value, U_(A), proportional to the first a.c. system voltage and from said control quantity, ΔX_(A), such as the output signal of a current regulator in the first station, in accordance with an equation:

    α.sub.A =arc cos ((ΔX.sub.A +U.sub.dB)/U.sub.A).


23. An apparatus according to claim 22, wherein said control quantity, ΔX_(A), is generated by summing an output signal of an active power controller having a set value, P*, applied; and the quotient of P*/U_(dB).
 24. An apparatus according to claim 21, further comprising:a control quantity controller, in the second station; computing elements, in said first computer circuit, to generate an extinction set value, γ*, from the set value of said control quantity controller, and said first automatic control quantity such as an automatic control angle:

    α.sub.Bv =180°-γ*-u

or an automatic control voltage:

    U.sub.dBv =U.sub.B cos γ*+2dX.sub.B ·i.sub.dB

wherein U_(B) is a measured actual value proportional to the second a.c. system voltage; i_(dB) is a measured value of the d.c. current flowing through the second converter; dX_(B) is a converter parameter for calculating the inductive d.c. voltage drop given by (-dx_(B) ·i_(dB))/U_(B) ; u is a precalculated overlap angle and for these quantities the relations hold:

    U.sub.B cos α.sub.Bv =-U.sub.dBv ;

and

    cos (180°-γ*-u)-cos (180°-γ*)=(-2·dx.sub.B ·i.sub.dB)/UB;

and a summing element, in said first automatic control unit, for adding the output of the control quantity controller and said first automatic control quantity, the output of said summing element being connected to the control circuit in the second station.
 25. An apparatus according to claim 24, further comprising comparative means comparing, following each thyristor firing of the second converter, a quantity derived from the actual extinction angle, with a quantity corresponding to the precalculated overlap angle u; and correcting the converter parameter, dX_(B), for precalculating said overlap angle.
 26. An apparatus according to claim 24, further comprising an second automatic control device located within and connected to the first station having a summing point connected to a control quantity generated in the control or regulating device of the first station; and an second automatic control quantity proportional to the measured or calculated HVDC voltage of the first station; whereby the control angle, of the first converter is generated as the sum of a preset angle correlated to said control quantity, and an automatic control angle, determined by said second automatic control quantity.
 27. An apparatus according to claim 26, further comprising a current regulator connected to the first station for regulating HVDC current, whereby said control quantity of the first station is obtained during normal operation from said current regulator.
 28. An apparatus according to claim 27, whereby said currrent regulator of the first station is optimized with respect to the time constant of the first station, and the control quantity controller of the second station is optimized to the time constant of the second station, whereby both said optimization are performed without regard for the other station or for the HVDC transmission line.
 29. An apparatus according to claim 27, whereby said control quantities and said automatic control quantities of each station are derived from preset and actual values generated in each station for that station without consideration of operating data obtained from the other station over remote control lines.
 30. An apparatus according to claim 26, further comprising:in each station a monitoring device is connected to the respective station, connecting to and monitoring the electrical quantities of the respective a.c. system, each said monitoring device generating: an internal malfunction signal in the case of a malfunction in the voltage of the directly connected a.c. system; an internal release signal in the case of return from the malfunction of the directly connected a.c. system; a derived malfunction signal in the case of a malfunction of the other station; and a derived release signal, in the case of resumption of normal operation of the other station, whereby: switching means in each respective station, return each said automatic control device to the start position after the occurrence of a malfunction signal in the respective station, and each said automatic control device, generates a control angle, for its respective converter, of approximately 90°, corresponding to a zero d.c. output voltage of its own converter; said switching means, following the occurrence of a release signal in its respective station, connecting a substitute automatic control quantity generated by a preset run-up function to the respective control device, in place of said automatic control quantity derived from measured momentary values; and said switching means switching once again from said respective substitute automatic control quantities to said respective automatic control quantities derived from momentary values when approximately attaining the limit value of the run-up function.
 31. An apparatus according to claim 30, whereby a run-up function generator in each said stations generates each said substitute automatic control quantity having an initial value of approximately 90 degrees for each said automatic control angle; and means capable of impressing a voltage pulse when starting each run-up function generator following an internal release signal of the HVDC transmission line which either precedes or overrides the start of each respective run-up function by a short-term shift toward rectifier operation.
 32. An apparatus according to claim 30, whereby said switching means of the respective stations disengage said control quantities of the respective station during the run-up.
 33. An apparatus according to claim 21, further comprising a linearizing element in series each with said automatic control device.
 34. An apparatus according to claim 21, further comprising:a preset extinction angle generator supplying a preset extinction angle, γ*; computing means generating an automatic control quantity; and a limiter connected to said computing means and the control circuit of the second station; said limiter thereby limiting the control angle of said control unit to an automatic control angle, α_(Bv), defined by said automatic control quantity; wherein for computing said automatic control quantity the following equations hold:

    α.sub.Bv =180°-γ*-u;

    U.sub.dBv =U.sub.B cos γ*+2dx·i.sub.dB ;

    U.sub.dBv =-U.sub.B cos α.sub.Bv ;

U_(B) being a measured instantaneous value proportional to the voltage amplitude of the second a.c. system; i_(dB) being the measured instantaneous value of the d.c. current flowing through the second converter; dx_(B) being a converter parameter of the second converter; U_(dBv) being a calculated automatic control voltage and u being precalculated overlap angle.
 35. An apparatus according to claim 21, further comprising: a control quantity controller, in the control or regulating device of the second station, having as an input one of the following signals: a transmitted active power signal; a transmitted reactive power signal; and a second a.c. system voltage signal. 